US20030066359A1 - Distributed sound speed measurements for multiphase flow measurement - Google Patents
Distributed sound speed measurements for multiphase flow measurement Download PDFInfo
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Definitions
- This invention relates to multiphase flow measurement systems to monitor multiphase flow production. More particularly the present invention incorporates sound speed measurements to fundamentally improve the ability of multiphase flow measurement systems to determine phase flow rates of a fluid.
- the numerous approaches to multiphase flow measurement of the prior art can typically be divided into two main categories of multiphase flow meters (MPFM's).
- the first category seeks to develop instruments to measure the oil/water/gas flow rates based on localized measurement. This is a typical industry approach in which a variety of measurements are made on the oil/gas/water mixture to help determine the flow rates of the individual components. This approach has focused on developing novel and robust instruments designed to provide precise multiphase flow measurements, such as dual-intensity gamma densitomers, microwave meters, capacitance and conductance meters, etc.
- MPFM's are a collection of several essentially separate, but co-located measurement devices that provide a sufficient number of measurements to uniquely determine the flow rate at the meter location.
- Prior art multiphase flow meter manufacturers for monitoring hydrocarbon production include Roxar, Framo, and Fluenta, among others.
- These MPFM's are typically restricted to operate above the well, either on the surface or subsea, for various reasons including reliability in the harsh environment and complications due to the presence of electrical power. Since the MPFM's typically operate at pressures and temperatures determined by production conditions and operators are typically interested in oil and gas production at standard conditions, the flow rates measured at the meter location are translated to standard conditions through fluid properties data (Pressure, Temperature, and Volumetric properties (PVT)).
- PVT Pressure, Temperature, and Volumetric properties
- the second category of prior art MPFM's provides multiphase flow rate information by utilizing measurements distributed over the production system in conjunction with a mathematical description, or model, of the production system.
- the mathematical model utilizes multiphase flow models to relate the parameters sought to estimates for the measured parameters.
- the flow rates are determined by adjusting the multiphase flow rates to minimize the error between the distributed measurements and those predicted by the mathematical model.
- the type, number, and location of the measurements that enter into this global minimization process to determine flow rates can vary greatly, with cost, reliability and accuracy all entering into determining the optimal system.
- the distributed measurement approaches are fundamentally rooted in the relationship between flow rates and pressure and temperature. Specifically, pressure drop in flow within a pipe is due primarily to viscous losses which are related to flow rate, and hydrostatic head changes which are related to changes in density of fluid and hence composition. Axial temperature gradients are primarily governed by the radial heat transfer from the flow within the production tubing into the formation as the flow is produced and is related to the heat capacity of the fluid, heat transfer coefficients, and the flow rate. The pressure drop and temperature losses are used to predict flow rates.
- the fundamental problem with this approach is that the relationship between flow rate and either of these two parameters is highly uncertain and often must be calibrated or tuned on a case-by-case basis. For instance, it is known that it is extremely difficult to accurately predict pressure drop in multiphase flow.
- phase fraction measurements and/or volumetric flow rate measurements are performed by auxiliary sensors that constrain the global optimization for specific variables at specific locations.
- the auxiliary sensors reduce the need for in-situ tuning of the optimization procedure required to produce accurate results.
- a multiphase flow measurement system incorporates fluid sound speed measurements into a multiphase flow model thereby fundamentally improving the system's ability to determine phase flow rates of a fluid.
- the distributed system includes at least one flow meter disposed along the pipe, an additional sensor disposed along the pipe spatially removed from the flow meter, and a multiphase flow model that receives the flow related parameters from the flow meter and the additional sensor to calculate the phase flow rates.
- the distributed system may utilize a plurality of flow meters disposed at several locations along the pipe and may further include a plurality of additional sensors as well.
- the distributed system preferably uses fiber optic sensors with Bragg gratings. This enables the system to have a high tolerance for long term exposure to harsh temperature environments and also provides the advantage of multiplexing the flow meters and/or sensors together.
- the flow meter provides parameters to the well bore model including pressure, temperature, velocity and sound speed of the fluid.
- the flow meter includes a pressure assembly and a flow assembly, which may be coupled together as a single assembly or separated into two subassemblies.
- the pressure assembly preferably contains a pressure sensor for measuring the pressure of the fluid and/or a temperature sensor for measuring the temperature of the fluid.
- the flow assembly preferably contains a fluid sound speed sensor for measuring the fluid sound speed and/or a velocity sensor for measuring the bulk velocity and volumetric flow rate of the fluid.
- the additional sensor along with the flow meter, provides the necessary parameters for the multiphase flow model to determine phase flow rates.
- the additional sensor is disposed along the pipe at a location, spatially removed, from the flow meter, preferably vertically removed, for e.g., downstream from the flow meter.
- the additional sensor may measure temperature, pressure or with a plurality of additional sensors measure both temperature and pressure. This measurement may be taken at the well head of the pipe, and preferably below the main choke valve.
- the measurements from the additional sensor and the flow meter are received by an optimization procedure which seeks to adjust the parameters of a multiphase flow model of the systems such that the error between the measurements recorded by the sensors and those simulated by the model is minimized.
- the parameters for which the error is minimized yields the desired flow rates.
- a variety of multiphase flow models may be used to determine the phase flow rates. Models have incorporated pressure and temperature measurements previously; however, the present invention incorporates a fluid sound speed measurement into the model which significantly improves the ability of the model to determine phase flow rates.
- FIG. 1 is a schematic diagram of a prior art multiphase flow meter
- FIG. 2 is a schematic diagram of a single zone multiphase flow meter in accordance with the present invention.
- FIG. 3 is a schematic block diagram of a sound speed measurement system, in accordance with one aspect of the present invention.
- FIG. 4 is a graph of the magnitude of the fluid sound speed estimate versus an error term over a range of frequencies, in accordance with one aspect of the present invention
- FIG. 5 is a portion of a logic flow diagram for measuring fluid sound speed, in accordance with one aspect of the present invention.
- FIG. 6 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location separated by a pair of Bragg gratings, in accordance with one aspect of the present invention
- FIG. 7 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location with a single Bragg grating between each pair of optical wraps, in accordance with one aspect of the present invention
- FIG. 8 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location without Bragg gratings, in accordance with one aspect of the present invention.
- FIG. 9 is an alternative geometry of an optical wrap of radiator tube geometry, in accordance with one aspect of the present invention.
- FIG. 10 is an alternative geometry of an optical wrap of a race track geometry, in accordance with one aspect of the present invention.
- FIG. 11 is a side view of a pipe having a pair of gratings at each axial sensing location, in accordance with one aspect of the present invention.
- FIG. 12 is a side view of a pipe having a single grating at each axial sensing location, in accordance with one aspect of the present invention.
- FIG. 13 is a schematic block diagram of a sound speed measurement system in an oil or gas well application, using fiber optic sensors, in accordance with one aspect of the present invention
- FIG. 14 is a graph of fluid sound speed versus the percent water volume fraction for an oil/water mixture, in accordance with one aspect of the present invention.
- FIG. 15 is a continuation of the logic flow diagram of FIG. 5 for measuring fluid sound speed, in accordance with one aspect of the present invention.
- FIG. 16 is a schematic block diagram of a velocity measurement system, in accordance with one aspect of the present invention.
- FIG. 17 is a side view of a pipe having two sensors that measure a vortical pressure in the pipe, as is known in the art;
- FIG. 18 is a graph of two curves, one from each of the two sensors of FIG. 17;
- FIG. 19 is a graph of a cross-correlation between the two curves of FIG. 18;
- FIG. 20 is a graph of power spectral density plotted against frequency for an unsteady acoustic pressure signal P acoustic and unsteady vortical pressure signal P vortical , in accordance with one aspect of the present invention
- FIG. 21 is a graph of power spectrum of two unsteady vortical pressures and the difference between the two pressures, in accordance with one aspect of the present invention.
- FIG. 22 is a graph of a cross-correlation between two of the curves of FIG. 21, in accordance with one aspect of the present invention.
- FIG. 23 is a graph of measured velocity against reference velocity, in accordance with one aspect of the present invention.
- FIG. 24 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location separated by a pair of Bragg gratings, in accordance with one aspect of the present invention.
- FIG. 25 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location with a single Bragg grating between each pair of optical wraps, in accordance with one aspect of the present invention
- FIG. 26 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location without Bragg gratings, in accordance with one aspect of the present invention.
- FIG. 27 is an alternative geometry of an optical wrap of a radiator tube geometry, in accordance with one aspect of the present invention.
- FIG. 28 is an alternative geometry of an optical wrap of a race track geometry, in accordance with one aspect of the present invention.
- FIG. 29 is a side view of a pipe having a pair of gratings at each axial sensing location, in accordance with one aspect of the present invention.
- FIG. 30 is a side view of a pipe having a single grating at each axial sensing location, in accordance with one aspect of the present invention.
- FIG. 31 is a schematic block diagram of a velocity measurement system in an oil or gas well application, using fiber optic sensors, in accordance with one aspect of the present invention.
- FIG. 32 is a representation of a single zone multiphase flow system in accordance with the present invention.
- FIG. 33 is a block diagram of a multiphase flow model in accordance with the present invention.
- FIG. 34 is a graph representing a numerical test of a multiphase flow model incorporating pressure and temperature measurements to determine Oil Rate
- FIG. 35 is a graph representing a numerical test of a multiphase flow model incorporating pressure and temperature measurements to determine Water Rate
- FIG. 36 is a graph of the error function created for a multiphase flow model incorporating pressure and temperature measurements to determine phase flow rates
- FIG. 37 is a graph representing a numerical test of a multiphase flow model incorporating sound speed, velocity and pressure measurements to determine Gas Rate;
- FIG. 38 is a graph representing a numerical test of a multiphase flow model incorporating sound speed, velocity and pressure measurements to determine Oil Rate;
- FIG. 39 is a graph representing a numerical test of a multiphase flow model incorporating sound speed, velocity and pressure measurements to determine Water Rate;
- FIG. 40 is a graph of the error function created for a multiphase flow model incorporating sound speed, velocity and pressure measurements to determine phase flow rates.
- FIG. 41 is a graphical representation of a multizone multiphase flow system in accordance with the present invention.
- FIG. 1 there is shown a prior art MPFM 10 for monitoring flow rates of a multi-phase fluid represented by arrow 12 flowing within a pipe 14 .
- Math model 16 of MPFM 10 utilizes output from sensor 18 and at least sensor 20 to predict the phase fraction flow rate of fluid 12 .
- Sensors 18 , 20 are typical prior art sensors described above that provide parameters to the model 16 such as temperature, pressure, and phase fraction.
- Model 16 utilizes the output of sensors 18 , 20 to determine, among other things, axial momentum and radial heat transfer of the fluid 12 . The axial momentum and radial heat transfer are calibrated to phase fraction volumetric flow rates at known conditions to provide an estimate of the global multi-phase flow rate Qw.
- FIG. 2 there is shown a MPFM 30 of the present invention, which utilizes sensor 32 and sensor 34 .
- Sensor 32 and sensor 34 may comprise a single sensor or a sensor system comprising multiple sensors or sensor arrays.
- Sensors 32 and 34 which include fiber optic or electronically passive sensors, provide temperature, pressure, sound speed measurements and/or bulk velocity measurements of a multi-phase fluid 12 to system model 16 .
- One sensor system referred to as a “flow meter,” that can be used to measure these parameters is disclosed in U.S. application Ser. No. 09/740,760, entitled “Apparatus for Sensing Fluid in a Pipe,” filed Nov. 29, 2000, which is incorporated herein by reference in its entirety.
- Model 16 utilizes the speed of sound and/or bulk velocity information to provide a robust and accurate multi-phase flow rate Qw to monitor multiphase flow production. Because the present invention preferably employs a fluid sound speed and fluid velocity, the methods for determining these parameters are disclosed in detail in the following sections.
- the present invention utilizes acoustic sensors 32 , 34 and methods such as that described in U.S. Pat. No. 6,354,147, entitled “Fluid Parameter Measurement in Pipes Using Acoustic Pressure,” which is incorporated herein by reference in its entirety, and discussed in further detail below.
- the sensors provide sound speed measurements to model 16 by measuring acoustic pressure waves in the fluid 12 .
- the invention preferably uses acoustic signals having lower frequencies (and thus longer wavelengths) than those used for ultrasonic meters, such as below about 20 kHz (depending on pipe diameter). Typically, for 3-7 inch production tubing, the desired frequency range is between 100-2000 hz.
- the invention is more tolerant to the introduction of gas, sand, slugs, or other inhomogeneities in the fluid.
- the embodiment described below may also be referred to as a phase fraction meter or sound speed meter.
- FIG. 3 discloses a speed of sound meter that could be used for either of the sensors 32 or 34 in FIG. 2.
- the pipe, or conduit, 14 has three unsteady pressure sensors 114 , 116 , 118 , located at three locations x 1 , x 2 , x 3 along the pipe 14 .
- the sensors 114 , 116 , 118 provide pressure time-varying signals P 1 (t), P 2 (t), P 3 (t) on lines 120 , 122 , 124 , to known Fast Fourier Transform (FFT) logics 126 , 128 , 130 , respectively.
- FFT Fast Fourier Transform
- the FFT logics 126 , 128 , 130 calculate the Fourier transform of the time-based input signals P 1 (t), P 2 (t), P 3 (t) and provide complex frequency domain (or frequency based) signals P 1 ( ⁇ ), P 2 ( ⁇ ), P 3 ( ⁇ ) on lines 132 , 134 , 136 indicative of the frequency content of the input signals.
- any other technique for obtaining the frequency domain characteristics of the signals P 1 (t), P 2 (t), P 3 (t) may be used.
- the cross-spectral density and the power spectral density may be used to form frequency domain transfer functions (or frequency responses or ratios) discussed below.
- the frequency signals P 1 ( ⁇ ), P 2 ( ⁇ ), P 3 ( ⁇ ) are fed to an a mix -Mx Calculation Logic 140 which provides a signal on a line 146 indicative of the speed of sound of the mixture a mix .
- the a mix signal is provided to map (or equation) logic 148 , which converts a mix to a percent composition of the fluid and provides a “% Comp” signal on line 150 .
- map (or equation) logic 148 which converts a mix to a percent composition of the fluid and provides a “% Comp” signal on line 150 .
- the calculation logic 140 may also provide a signal Mx on a line 159 indicative of the Mach number (as discussed below).
- the acoustic pressure field P(x,t) at a location x along a pipe where the wavelength ⁇ of the acoustic waves to be measured is long compared to the diameter d of the pipe 14 (i.e., ⁇ /d>>1), may be expressed as a superposition of a right traveling wave and a left traveling wave, as follows:
- a mix is the speed of sound in the mixture in the pipe
- ⁇ is frequency (in rad/sec)
- M x is the axial Mach number of the flow of the mixture within the pipe, where: M x ⁇ V m ⁇ ⁇ i ⁇ ⁇ x a m ⁇ ⁇ i ⁇ ⁇ x Eq . ⁇ 3
- V mix is the axial velocity of the mixture.
- the axial Mach number represents the average velocity of the mixture and the low frequency acoustic field description remains substantially unaltered.
- the frequency domain representation P(x, ⁇ ) of the time-based acoustic pressure field P(x,t) within a pipe is the coefficient of the e i ⁇ t term of Eq. 1:
- a and B are arbitrary constants describing the acoustic field between the sensors 114 , 116 , 118 .
- R ⁇ B A ⁇ - ⁇ ⁇ ⁇ k r ⁇ x 1 - [ P 1 ⁇ ( ⁇ ) P 2 ⁇ ( ⁇ ) ] ⁇ ⁇ - ⁇ ⁇ ⁇ k r ⁇ x 2 [ P 1 ⁇ ( ⁇ ) P 2 ⁇ ( ⁇ ) ] ⁇ ⁇ ⁇ ⁇ ⁇ k i ⁇ x 2 - ⁇ ⁇ ⁇ ⁇ k i ⁇ x 1 Eq . ⁇ 8
- R is defined as the reflection coefficient
- Eq. 9 may be solved numerically, for example, by defining an “error” or residual term as the magnitude of the left side of Eq. 9, and iterating to minimize the error term.
- the speed of sound in the fluid may be computed by either: (1) varying a mix while minimizing an error term, (2) calculating a logarithmic relationship between the acoustic pressure variation signals, or (3) calculating a trigonometric relationship between the acoustic pressure variation signals.
- the axial velocity of the flow in the pipe is small compared to the speed of sound in the mixture (i.e., the axial Mach number M x is small compared to one).
- the axial velocity of the oil V oil in a typical oil well is about 10 ft/sec and the speed of sound in oil a oil is about 4,000 ft/sec.
- the error term of Eq. 10 constitutes a family of curves, one curve for each frequency ⁇ , where the value of the error is evaluated for values of a mix varied from a water (5,000 ft/sec) to a oil (4,000 ft/sec) at each frequency varied from 5 to 200 Hz in 5 Hz increments. Other frequencies may be used if desired.
- the speed of sound a mix where the error goes to zero (or is minimized) is the same for each frequency ⁇ evaluated. In this case, the error is minimized at a point 170 when a mix is 4335 ft/sec.
- Eq. 14 is particularly useful due to its simple geometric form, from which a mix can be easily interpreted.
- a mix can be determined directly by inspection from a digital signal analyzer (or other similar instrument) set up to provide a display indicative of the left side of Eq. 14, which will be a cosine curve from which a mix may be readily obtained. For example, at the zero crossing of the cosine wave, a mix will be equal to 2 ⁇ X/ ⁇ .
- Eq. 14 may be used to determine a mix using an iterative approach where a measured function is calculated from the left side of Eq. 14 (using the measured pressures), which is compared to a cosine curve of the right side of Eq. 14, where a mix is varied until it substantially matches the measured function.
- Various other curve fitting, parameter identification, and/or minimum error or solution techniques may be used to determine the value of a mix that provides the best fit to satisfy Eq. 14.
- the calculation logic 140 begins at step 200 where P 12 is calculated as the ratio of P 1 ( ⁇ )/P 2 ( ⁇ ), and at step 202 where P 13 is calculated as the ratio of P 1 ( ⁇ )/P 3 ( ⁇ ).
- step 208 calculates a mix (n) from the closed form solution of Eq. 13.
- step 210 checks whether the logic 140 has calculated a mix at a predetermined number of frequencies, e.g., 10. If n is not greater than 10, steps 212 and 214 increment the counter n by one and increases the frequency ⁇ by a predetermined amount (e.g., 10 Hz) and step 208 is repeated. If the logic 140 has calculated a mix at 10 frequencies, logic 140 goes to step 216 , which determines an average value for a mix using the values of a mix (n) over the 10 frequencies, and the logic 140 then exits.
- a predetermined number of frequencies e.g. 10 Hz
- step 232 checks whether n is greater than or equal to 10. If not, step 234 increments n by one and step 236 increases the frequency ⁇ by a predetermined amount (e.g., 10 Hz) and continues at step 222 as shown in FIG. 15. If n is greater than or equal to 10, step 238 calculates an average value for a mix over the 10 frequencies, and the logic 140 ends.
- a predetermined amount e.g. 10 Hz
- step 306 calculates the error term of Eq. 10.
- step 312 increases a mix by a predetermined amount (e.g., 1 ft/sec) and the logic goes back to step 306 . If the result of step 310 is yes, step 314 increases Mx by a predetermined amount (e.g., 1) and the logic goes back to step 304 .
- a predetermined amount e.g. 1 ft/sec
- pairs of Bragg gratings ( 410 , 412 ), ( 414 , 416 ), ( 418 , 420 ) may be located along the fiber 400 at opposite ends of each of the wraps 402 , 404 , 406 , respectively.
- the grating pairs are used to multiplex the pressure signals P 1 , P 2 , P 3 to identify the individual wraps from optical return signals.
- the first pair of gratings 410 , 412 around the wrap 402 may have a common reflection wavelength ⁇ 1
- the second pair of gratings 414 , 416 around the wrap 404 may have a common reflection wavelength ⁇ 2 , but different from that of the first pair of gratings 410 , 412
- the third pair of gratings 418 , 420 around the wrap 406 have a common reflection wavelength ⁇ 3 , which is different from ⁇ 1 and ⁇ 2 .
- the fiber 400 may continue to other sensors as shown by reference numeral 17 or return the optical signals to the instrument as shown by reference numeral 15 .
- a series of Bragg gratings 460 , 462 , 464 , 466 with only one grating between each of the wraps 402 , 404 , 406 may be used, each having a common reflection wavelength ⁇ 1 .
- the wraps 402 , 404 , 406 with the gratings 410 , 412 , 414 , 416 , 418 , 420 (FIG. 22) or with the gratings 460 , 462 , 464 , 466 (FIG. 7) may be configured in numerous known ways to precisely measure the fiber length or change in fiber length, such as by interferometric, Fabry Perot, time-of-flight, or other known arrangements.
- time-of-flight or Time-Division-Multiplexing; TDM
- TDM Time-Division-Multiplexing
- the gratings are shown oriented axially with respect to pipe 14 in FIGS. 6 and 7, the gratings may be oriented along the pipe 14 axially, circumferentially, or in any other orientations. Depending on the orientation, the grating may measure deformations in the pipe wall with varying levels of sensitivity. If the grating reflection wavelength varies with internal pressure changes, such variation may be desired for certain configurations (e.g., fiber lasers) or may be compensated for in the optical instrumentation for other configurations, e.g., by allowing for a predetermined range in reflection wavelength shift for each pair of gratings. Alternatively, instead of each of the wraps being connected in series, they may be connected in parallel, e.g., by using optical couplers (not shown) prior to each of the wraps, each coupled to the common fiber 400 .
- optical couplers not shown
- the sensors 114 , 116 , 118 may also be formed as a purely interferometric sensor by wrapping the pipe 14 with the wraps 402 , 404 , 406 without using Bragg gratings, in which case separate fibers 430 , 432 , 434 may be fed to the separate, corresponding wraps 402 , 404 , 406 .
- known interferometric techniques may be used to determine the length or change in length of the fiber wraps 402 , 404 , 406 around the pipe 14 due to pressure changes within the pipe. These known interferometric techniques include the Mach Zehnder or Michaelson Interferometric techniques that are described in U.S. Pat. No.
- the wraps 402 , 404 , 406 may have alternative geometries, such as a “radiator coil” geometry, as shown in FIG. 9, or a “race-track” geometry, as shown in FIG. 10. Both of these alternative geometries are shown in a side view as if the pipe 14 is cut axially and laid flat.
- the wraps 402 , 404 , 406 are not necessarily wrapped 360 degrees around the pipe, but may be disposed over a predetermined portion of the circumference of the pipe 14 with a length long enough to optically detect the changes to the pipe circumference.
- wraps may be used if desired. Also, for any geometry of the wraps described, more than one layer of fiber may be used depending on the overall fiber length desired.
- the desired axial length of any particular wrap is set depending on the characteristics of the ac pressure desired to be measured, for example the axial length of the pressure disturbance caused by a vortex to be measured.
- embodiments of the present invention include configurations wherein instead of using the wraps 402 , 404 , 406 , the fiber 400 may have shorter sections that are disposed around at least a portion of the circumference of the pipe 14 that can optically detect changes to the pipe circumference. It is further within the scope of the present invention that sensors may comprise an optical fiber 400 disposed in a helical pattern (not shown) about pipe 14 . As discussed above, the orientation of the strain sensing element will vary the sensitivity to deflections in pipe wall deformations caused by unsteady pressure signals in the pipe 14 .
- FIG. 13 illustrates an embodiment of a sound speed measurement system in an oil or gas well application.
- the sensing section 151 may be connected to or part of the production tubing 602 (analogous to the pipe 14 in the test section 151 ) within a well 600 .
- An isolation sleeve 510 may be located over the sensors 114 , 116 , 118 and attached to the pipe 602 at its axial ends to protect the sensors 114 , 116 , 118 (or fibers) from damage during deployment, use, or retrieval.
- the isolation sleeve may also help isolate the sensors 114 , 116 , 118 from acoustic external pressure effects that may exist outside the pipe 602 , and/or to help isolate ac pressures in the pipe 602 from ac pressures outside the pipe 602 .
- the sensors 114 , 116 , 118 are connected to a cable 606 which may comprise an optical fiber 400 and is connected to a transceiver/converter 610 located outside the well 600 .
- the transceiver/converter 610 may be used to receive and transmit optical signals 604 to the sensors 114 , 116 , 118 and provides output signals indicative of the pressure P 1 , P 2 , P 3 at the sensors 114 , 116 , 118 on the lines 120 , 122 , 124 , respectively. Also, the transceiver/converter 610 may be part of the Fluid Parameter Logic 160 . The transceiver/converter 610 may be any device that performs the corresponding functions described.
- the transceiver/converter 610 together with the optical sensors described above may use any type of optical grating-based measurement technique, e.g., scanning interferometric, scanning Fabry Perot, acousto-optic-tuned filter (AOTF), optical filter, time-of-flight, and may use WDM and/or TDM, etc., having sufficient sensitivity to measure the ac pressures within the pipe, such as that described in one or more of the following references: A. Kersey et al., “Multiplexed fiber Bragg grating strain-sensor system with a Fabry-Perot wavelength filter,” Opt. Letters, Vol. 18, No. 16, August 1993; U.S. Pat. No.
- sensors 32 , 34 provide sound speed measurements, by the method described above, which significantly enhance phase fraction determination over that of the prior art.
- Prior art phase fraction meters microwave, dual beam densitometer, etc.
- An advantage of the present invention is that a sound speed measurement does not uniquely determine the phase fractions, but rather provides a constraint on a combination of the phase fractions.
- sound speed measurements are analogous to density measurements.
- the density of a well-mixed mixture of oil, water, and gas (immiscible mixture) is related to the phase fraction and the density of the individual components via the following relation:
- ⁇ is the density of the mix or constituent of the multi-component mixture
- a is the sound speed of the mix or constituent of the mixture
- ⁇ is the volumetric phase fraction of the mix or constituent of the mixture.
- a curve 110 shows the speed of sound in the mixture a mix plotted as a function of water volume fraction.
- the values used for density (p) and speed of sound (a) in oil and water are as follows:
- the present invention can be used to measure fluid volume fractions of a mixture of any number of fluids in which the speed of sound of the mixture a mix is related to (or is substantially determined by) the volume fractions of two constituents of the mixture, e.g., oil/water, oil/gas, water/gas.
- the present invention can be used to measure the speed of sound of any mixture and can then be used in combination with other known quantities to derive phase content of mixtures with multiple (more than two) constituents.
- the present invention further includes velocity sensors 32 , 34 and methods for determining bulk velocity or volumetric flow rates such as that described in U.S. patent application Ser. No. 09/346,607, entitled, “Flow Rate Measurement Using Unsteady Pressures,” filed Jul. 2, 1999, which is incorporated herein by reference in its entirety, and discussed in further detail below. Similar to that described previously with regard to sound speed measurements, the volumetric flow rate based on a cross correlation based flow rate measurement significantly improves distributed measurement flow rate determination utilizing model 16 . For well-mixed flows of fluid 12 within a pipe 14 , a homogeneous model 16 which assumes that all the phases are flowing at the same velocity may be sufficient.
- slip models may be required to translate flow velocities provided from cross correlation measurements into individual component flow rates.
- the present invention incorporates cross correlation measurements that improve the predictive performance of the model 16 for multi-phase flow Qw information.
- the sensors provide bulk velocity measurement to model 16 (FIG. 2) by measuring vortical pressures in the fluid.
- FIG. 2 the embodiment described below may be referred to as a flow meter.
- a velocity and flow measurement system includes a sensing section 710 along a pipe, or conduit, 14 and a velocity logic section 740 .
- the pipe 14 has two measurement regions 714 , 716 located a distance ⁇ X apart along the pipe 14 .
- At the first measurement region 714 are two unsteady (or dynamic or ac) pressure sensors 718 , 720 , located a distance X 1 apart, capable of measuring unsteady vortical pressures in the pipe 14
- the second measurement region 716 are two other unsteady pressure sensors 722 , 724 , located a distance X 2 apart, also capable of measuring unsteady vortical pressures in the pipe 14 .
- Each pair of pressure sensors 718 , 720 and 722 , 724 act as spatial filters to remove certain acoustic signals from the unsteady pressure signals, and the distances X 1 , X 2 are determined by the desired filtering characteristic for each spatial filter, as discussed hereinafter.
- the flow measurement system 710 of the present invention measures velocities associated with unsteady flow fields and/or pressure disturbances represented by 715 such as turbulent eddies (or vortical flow fields), inhomogeneities in the flow (such as bubbles, slugs, and the like), or any other properties of the flow, fluid, or pressure, having time varying or stochastic properties in the form of unsteady pressures.
- the vortical flow fields 715 are, in general, comprised of pressure disturbances having a wide variation in length scales and which have a variety of coherence length scales such as that described in the reference “Sound and Sources of Sound,” A. P. Dowling et al, Halsted Press, 1983.
- Vortical flow fields often convect at or near the mean velocity of at least one of the fluids within a mixture flowing in a pipe. More specifically, the vortices convect in a predictable manner with reference to the fluids.
- the vortical pressure disturbances 715 that contain information regarding convection velocity have temporal and spatial length scales as well as coherence length scales that differ from other disturbances in the flow.
- the present invention utilizes these properties to preferentially select disturbances of a desired axial length scale and coherence length scale as will be more fully described hereinafter.
- the terms vortical flow field and vortical pressure field will be used to describe the above-described group of unsteady pressure fields having temporal and spatial length and coherence scales described.
- the pressures P 1 , P 2 , P 3 , P 4 may be measured through holes in the pipe 14 ported to external pressure sensors or by other techniques discussed hereinafter.
- the pressure sensors 718 , 720 , 722 , 724 provide time-based pressure signals P 1 (t), P 2 (t), P 3 (t), P 4 (t) on lines 730 , 732 , 734 , 736 , respectively, to Velocity Logic 740 which provides a convection velocity signal U c (t) on a line 742 which is related to an average flow rate U f (t) of the fluid flowing in the pipe 14 (where fluid may comprise one or more liquids and/or gases; where the gas(es) may be dissolved in the liquid or in free gas form, and wherein the fluid may include non-liquid elements).
- the pressure signal P 1 (t) on the line 730 is provided to a positive input of a summer 744 and the pressure signal P 2 (t) on the line 732 is provided to a negative input of the summer 744 .
- the line 745 is fed to bandpass filter 746 , which passes a predetermined passband of frequencies and attenuates frequencies outside the passband.
- the passband of the filter 746 is set to filter out (or attenuate) the dc portion and the high frequency portion of the input signals and to pass the frequencies therebetween.
- bandpass filter 746 is set to pass frequencies from about 1 Hz to about 100 Hz, for a 3 inch ID pipe flowing water at 10 ft/sec. Other passbands may be used in other embodiments, if desired.
- Bandpass filter 746 provides a filtered signal P asf1 on a line 748 to Cross-Correlation Logic 750 , described below.
- the pressure signal P 3 (t) on the line 734 is provided to a positive input of a summer 754 and the pressure signal P 4 (t) on the line 736 is provided to a negative input of the summer 754 .
- the pressure sensors 722 , 724 together with the summer 754 create a spatial filter 735 .
- the line 755 is fed to a bandpass filter 756 , similar to the bandpass filter 746 discussed hereinbefore, which passes frequencies within the passband and attenuates frequencies outside the passband.
- the filter 756 provides a filtered signal P asf2 on a line 758 to the Cross-Correlation Logic 750 .
- the signs on the summers 744 , 754 may be swapped if desired, provided the signs of both summers 744 , 754 are swapped together.
- the pressure signals P 1 , P 2 , P 3 , P 4 may be scaled prior to presentation to the summers 744 , 754 .
- the Cross-Correlation Logic 750 calculates a known time domain cross-correlation between the signals P asf1 and P asf2 on the lines 748 , 758 , respectively, and provides an output signal on a line 760 indicative of the time delay T it takes for an vortical flow field 715 (or vortex, stochastic, or vortical structure, field, disturbance or perturbation within the flow) to propagate from one sensing region 714 to the other sensing region 716 .
- vortical flow disturbances are coherent dynamic conditions that can occur in the flow which substantially decay (by a predetermined amount) over a predetermined distance (or coherence length) and convect (or flow) at or near the average velocity of the fluid flow.
- the vortical flow field 715 also has a stochastic or vortical pressure disturbance associated with it.
- the vortical flow disturbances 715 are distributed throughout the flow, particularly in high shear regions, such as boundary layers (e.g., along the inner wall of the pipe 14 ) and are shown as discrete vortical flow fields 715 . Because the vortical flow fields 715 (and the associated pressure disturbance) convect at or near the mean flow velocity, the propagation time delay T is related to the velocity of the flow by the distance ⁇ X between the measurement regions 714 , 716 , as discussed below.
- a spacing signal ⁇ X on a line 762 indicative of the distance ⁇ X between the sensing regions 714 , 716 is divided by the time delay signal T on the line 760 by a divider 764 which provides an output signal on the line 742 indicative of the convection velocity U c (t) of the fluid flowing in the pipe 14 , which is related to (or proportional to or approximately equal to) the average (or mean) flow velocity U f (t) of the fluid, as defined below:
- the convection velocity U c (t) may then be calibrated to more precisely determine the mean velocity U f (t) if desired.
- the result of such calibration may require multiplying the value of the convection velocity U c (t) by a calibration constant (gain) and/or adding a calibration offset to obtain the mean flow velocity U f (t) with the desired accuracy. For some applications, such calibration may not be required to meet the desired accuracy.
- the velocities U f (t), U c (t) may be converted to volumetric flow rate by multiplying the velocity by the cross-sectional area of the pipe.
- cross-correlation may be used to determine the time delay ⁇ between two signals y 1 (t), y 2 (t) separated by a known distance ⁇ X, that are indicative of quantities 780 that convect with the flow (e.g., density perturbations, concentration perturbations, temperature perturbations, vortical pressure disturbances, and other quantities).
- quantities 780 that convect with the flow
- the signal y 2 (t) lags behind the signal y 1 (t) by 0.15 seconds.
- a time domain cross-correlation is taken between the two signals y 1 (t), y 2 (t)
- the result is shown in FIG. 19 as a curve 784 .
- the highest peak 786 of the curve 784 shows the best fit for the time lag ⁇ between the two signals y 1 (t), y 2 (t) is at 0.15 seconds which matches the reference time delay shown in FIG. 18.
- the vortical pressure disturbances observed at the downstream location 716 are substantially a time lagged version of the vortical pressure disturbances observed at the upstream location 714 .
- the total vortical pressure perturbations or disturbances in a pipe may be expressed as being comprised of vortical pressure disturbances (P vortical ), acoustic pressure disturbances (P acoustic ) and other types of pressure disturbances (P other ) as shown below expressed in terms of axial position along the pipe at any point in time:
- the unsteady pressure disturbances P vortical can be masked by the acoustic pressure disturbances P acoustic and the other types of pressure disturbances P other .
- the presence of the acoustic pressure disturbances that propagate both upstream and downstream at the speed of sound in the fluid (sonic velocity) can prohibit the direct measurement of velocity from cross-correlation of direct vortical pressure measurements.
- the present invention uses temporal and spatial filtering to precondition the pressure signals to effectively filter out the acoustic pressure disturbances P acoustic and other long wavelength (compared to the sensor spacing) pressure disturbances in the pipe 14 at the two sensing regions 714 , 716 and retain a substantial portion of the vortical pressure disturbances P vortical associated with the vortical flow field 715 and any other short wavelength (compared to the sensor spacing) low frequency pressure disturbances P other .
- the low frequency pressure disturbances P other are small, they will not substantially impair the measurement accuracy of P vortical .
- the P vortical dominated signals from the two regions 714 , 716 are then cross-correlated to determine the time delay ⁇ between the two sensing locations 714 , 716 . More specifically, at the sensing region 714 , the difference between the two pressure sensors 718 , 720 creates a spatial filter 733 that effectively filters out (or attenuates) acoustic disturbances for which the wavelength ⁇ of the acoustic waves propagating along the fluid is long (e.g., ten-to-one) compared to the spacing X 1 between the sensors. Likewise the same is true for spatial filter 735 . Other wavelength to sensor spacing ratios may be used to characterize the filtering, provided the wavelength to sensor spacing ratio is sufficient to satisfy the two-to-one spatial aliasing Nyquist criteria.
- PSD power spectral density
- a curve 790 that has a flat region (or bandwidth) up to a frequency F v and then decreases with increasing frequency f.
- the value of F v is approximately equal to U/r, where U is the flow rate and r is the radius of the pipe.
- U is the flow rate
- r is the radius of the pipe.
- the bandwidth F v of the vortical pressure disturbances P vortical would be about 80 Hz (10/0.125).
- the PSD of the acoustic pressure disturbances P acoustic has a profile that is determined by the environment and other factors and is indicated in the figure by an arbitrary curve 791 , and typically has both low and high frequency components.
- the acoustic spatial filters 733 , 735 discussed hereinbefore block or attenuate wavelengths longer than ⁇ as and frequencies below f as , as indicated by the region 796 .
- the bandpass filters (BPF) 746 , 756 (FIG. 16) block or attenuate high frequencies above f pb having short and long wavelengths and pass frequencies below f as where the P vortical signals exist.
- the resultant filtered signals P asf , P as12 on the lines 748 , 758 (FIG. 16) will be dominated by the short wavelength unsteady pressure disturbances P Vortical at frequencies below f pb and as indicated by a portion 794 of the curve 790 in the BPF passband 795 (FIG. 20).
- the spatial filters 733 , 735 (FIG. 16) block the long wavelengths, which, for the acoustic pressure disturbances P acoustic , occur at low frequencies as indicated to the left of a dashed line 792 at frequencies below the frequency f as .
- a dashed line 793 indicates the attenuation of the acoustic pressure P acoustic signal 791 below the frequency f as at the output of the spatial filters.
- the vortical pressure disturbances P vortical are substantially not attenuated (or only slightly attenuated) because P vortical has short wavelengths at low frequencies that are substantially passed by the spatial filter.
- the BPF's 746 , 756 (FIG. 16) block or attenuate frequencies outside the passband indicated by a range of frequencies 795 , and passes the unsteady pressure disturbances associated with stochastic flow fields 715 (FIG. 16) within the passband 795 .
- the filters 746 , 756 may comprise low pass filters, having a bandwidth similar to the upper band of the high pass filters discussed hereinbefore. If a low pass filter is used as the filters 746 , 756 , the passband is shown as a range of frequencies 789 . It should be understood that the filters 746 , 756 are not required for the present invention if the PSD of the acoustic pressure disturbances P acoustic has substantially no or low PSD energy content in frequencies above the stopband of the spatial filter that does not adversely affect the measurement accuracy.
- the power spectrum of the difference P as1 , between the two signals P 1 , P 2 , shown by a curve 804 is reduced in certain frequency bands (e.g., 100-150 Hz) and increased in other frequency bands (e.g., 200-250 Hz) as compared to the individual signals 800 , 802 .
- the cross correlation between the signals P as1 (or P 1 ⁇ P 2 ) and P as2 (P 3 ⁇ P 4 ) is shown as a curve 810 .
- the highest peak 812 indicates the best fit for the time lag between the two signals P as1 , P as2 as 0.015 seconds.
- the effective distance ⁇ X between the sensor pairs is 2 inches.
- the velocity measured from Eq. 18 is 11.1 ft/sec (2/12/0.015) using the present invention and the actual velocity was 11.2 ft/sec.
- FIG. 23 for the configuration described with FIGS. 16, 21, 22 above, the velocity was measured at various flow rates and plotted against a reference velocity value.
- a solid line 820 shows the reference velocity
- the triangles 822 are the measured data
- a line 824 is a curve fit of the data 822 . This illustrates that the present invention predicts the flow velocity within a pipe (or conduit).
- the ac pressure sensors 718 - 724 may be configured using an optical fiber 900 that is coiled or wrapped around and attached to the pipe 14 at each of the pressure sensor locations as indicated by the coils or wraps 902 , 904 , 906 , 908 for the pressures P 1 , P 2 , P 3 , P 4 , respectively.
- the fiber wraps 902 - 908 are wrapped around the pipe 14 such that the length of each of the fiber wraps 902 - 908 changes with changes in the pipe loop strain in response to unsteady pressure variations within the pipe 14 and thus internal pipe pressure is measured at the respective axial location.
- Each of the wraps measures substantially the circumferentially averaged pressure within the pipe 14 at a corresponding axial location on the pipe 14 . Also, the wraps provide axially averaged pressure over the axial length of a given wrap. While the structure of the pipe 14 provides some spatial filtering of short wavelength disturbances, we have found that the basic principle of operation of the invention remains substantially the same as that for the point sensors described previously.
- pairs of Bragg gratings ( 910 , 912 ), ( 914 , 916 ), ( 918 , 920 ), ( 922 , 924 ) may be located along the fiber 900 at opposite ends of each of the wraps 902 , 904 , 906 , 908 , respectively.
- the grating pairs are used to multiplex the pressure signals P 1 , P 2 , P 3 , P 4 to identify the individual wraps from optical return signals.
- the first pair of gratings 910 , 912 around the wrap 902 may have a common reflection wavelength ⁇ 1
- the second pair of gratings 914 , 916 around the wrap 904 may have a common reflection wavelength ⁇ 2 , but different from that of the first pair of gratings 910 , 912
- the third pair of gratings 918 , 920 around the wrap 906 have a common reflection wavelength ⁇ 3 , which is different from ⁇ 1 , ⁇ 2
- the fourth pair of gratings 922 , 924 around the wrap 908 have a common reflection wavelength ⁇ 4 , which is different from ⁇ 1 , ⁇ 2 , ⁇ 3
- the fiber 400 may continue to other sensors as shown by reference numeral 17 or return the optical signals to the instrument as shown by reference numeral 15 .
- a series of Bragg gratings 960 - 968 with only one grating between each of the wraps 902 - 908 may be used each having a common reflection wavelength ⁇ 1 .
- the wraps 902 - 908 with the gratings 910 - 924 (FIG. 24) or with the gratings 960 - 968 (FIG. 25) may be configured in numerous known ways to precisely measure the fiber length or change in fiber length, such as an interferometric, Fabry Perot, time-of-flight, or other known arrangements.
- An example of a Fabry Perot technique is described in U.S. Pat. No. 4,950,883, entitled “Fiber Optic Sensor Arrangement Having Reflective Gratings Responsive to Particular Wavelengths,” to Glenn.
- time-of-flight or Time-Division-Multiplexing; TDM
- TDM Time-Division-Multiplexing
- the gratings 910 - 924 are shown oriented axially with respect to the pipe 14 , in FIGS. 24 and 25, they may be oriented along the pipe 14 axially, circumferentially, or in any other orientations. Depending on the orientation, the grating may measure deformations in the pipe wall 952 with varying levels of sensitivity. If the grating reflection wavelength varies with internal pressure changes, such variation may be desired for certain configurations (e.g., fiber lasers) or may be compensated for in the optical instrumentation for other configurations, e.g., by allowing for a predetermined range in reflection wavelength shift for each pair of gratings. Alternatively, instead of each of the wraps being connected in series, they may be connected in parallel, e.g., by using optical couplers (not shown) prior to each of the wraps, each coupled to the common fiber 900 .
- optical couplers not shown
- the sensors 718 - 724 may also be formed as individual non-multiplexed interferometric sensor by wrapping the pipe 14 with the wraps 902 - 908 without using Bragg gratings where separate fibers 930 , 932 , 934 , 936 may be fed to the separate wraps 902 , 904 , 906 , 908 , respectively.
- known interferometric techniques may be used to determine the length or change in length of the fiber 710 around the pipe 14 due to pressure changes, such as Mach Zehnder or Michaelson Interferometric techniques, such as that described in U.S. Pat. No. 5,218,197, entitled “Method And Apparatus For The Non-Invasive Measurement Of Pressure Inside Pipes Using A Fiber Optic Interferometer Sensor,” to Carroll.
- the interferometric wraps may be multiplexed such as is described in Dandridge, et al, “Fiber Optic Sensors for Navy Applications,” IEEE, February 1991, or Dandridge, et al, “Multiplexed Interferometric Fiber Sensor Arrays,” SPIE, Vol. 1586, 1991, pp. 176-183. Other techniques to determine the change in fiber length may be used. Also, reference optical coils (not shown) may be used for certain interferometric approaches and may also be located on or around the pipe 14 but may be designed to be insensitive to pressure variations.
- the wraps 902 - 908 may have alternative geometries, such as a “radiator coil” geometry (FIG. 27) or a “race-track” geometry (FIG. 28), which are shown in a side view as if the pipe 14 is cut axially and laid flat.
- the wraps 902 - 908 are not necessarily wrapped 360 degrees around the pipe, but may be disposed over a predetermined portion of the circumference of the pipe 14 , and have a length long enough to optically detect the changes to the pipe circumference. Other geometries for the wraps may be used if desired.
- any geometry of the wraps described more than one layer of fiber may be used depending on the overall fiber length desired.
- the desired axial length of any particular wrap is set depending on the characteristics of the ac pressure desired to be measured, for example the axial length of the pressure disturbance caused by a vortex to be measured.
- the fiber 900 may have shorter sections that are disposed around at least a portion of the circumference of the pipe 14 that can optically detect changes to the pipe circumference.
- sensors may comprise an optical fiber 900 disposed in a helical pattern (not shown) about pipe 14 .
- the orientation of the strain sensing element will vary the sensitivity to deflections in pipe wall 952 caused by unsteady pressure transients in the pipe 14 .
- the pairs of Bragg gratings ( 910 , 912 ), ( 914 , 916 ), ( 918 , 920 ), ( 922 , 924 ) are located along the fiber 900 with sections 980 - 986 of the fiber 900 between each of the grating pairs, respectively.
- known Fabry Perot, interferometric, time-of-flight or fiber laser sensing techniques may be used to measure the strain in the pipe, in a manner similar to that described in the aforementioned references.
- individual gratings 970 - 976 may be disposed on the pipe and used to sense the unsteady variations in strain in the pipe 14 (and thus the unsteady pressure within the pipe) at the sensing locations.
- the grating reflection wavelength shift will be indicative of changes in pipe diameter and thus pressure.
- optical strain gage technique Any other technique or configuration for an optical strain gage may be used.
- the type of optical strain gage technique and optical signal analysis approach is not critical to the present invention, and the scope of the invention is not intended to be limited to any particular technique or approach.
- the present invention will also work over a wide range of oil/water/gas mixtures. Also, the invention will work for very low flow velocities, e.g., at or below 1 ft/sec (or about 20.03 gal/min, in a 3 inch diameter ID pipe) and has no maximum flow rate limit. Further, the invention will work with the pipe 14 being oriented vertical, horizontal, or any other orientation. Also the invention will work equally well independent of the direction of the flow along the pipe 14 .
- the thickness and rigidity of the outer wall of the pipe 14 is related to the acceptable spacing X 1 (FIG. 1) between the sensors 718 , 720 of the spatial filter 733 . More specifically, the thinner or less rigid the pipe 14 wall, the closer the sensors 718 , 720 can be to each other.
- the distance X 1 between the two sensors 718 , 720 should be larger than the spatial length of the vortical pressure field 715 such that each of the sensors 718 , 720 can independently measure the propagating vortical pressure field 715 between the sensors 718 , 720 at different times (such that the spatial filter 733 output is not zero for the measured vortex 715 ). Also, the distance X 1 should be within the coherence length of the vortex 715 such that the spatial filter output is indicative of a measured vortex 715 . Also, for optimal performance, the overall length L 1 between the first sensor 718 and the last sensor 724 of the velocity sensing section should be within the coherence length of the vortices 715 desired to be measured.
- the coherence length of the vortical flow field 715 is the length over which the vortical flow field remains substantially coherent, which is related to and scales with the diameter of the pipe 14 .
- Vortices that are sensed by only one of the spatial filters because either a vortex is generated between the spatial filters or generated outside the spatial filters and decay between them, will be substantially random events (in time and location) that will not be correlated to the vortices that are sensed by and continuously occurring past both spatial filters and, as such, will not significantly affect the accuracy of the measurement.
- FIG. 31 illustrates an embodiment of a velocity measurement system in an oil or gas well application.
- the sensing section 710 may be connected to or part of production tubing 502 within a well 500 .
- An outer housing, sheath, or cover 522 may be located over the sensors 718 - 724 and attached to the pipe (not shown) at the axial ends to protect the sensors 718 - 724 (or fibers) from damage during deployment, use, or retrieval, and/or to help isolate the sensors from external pressure effects that may exist outside the pipe 14 , and/or to help isolate ac pressures in the pipe 14 from ac pressures outside the pipe 14 .
- the sensors 718 - 724 are connected to a cable 506 which may comprise the optical fiber 900 (FIG. 16) and is connected to a transceiver/converter 520 located outside the well.
- the transceiver/converter 520 may be used to receive and transmit optical signals to the sensors 718 - 724 and provides output signals indicative of the pressure P 1 -P 4 at the sensors 18 - 24 on the lines 730 - 736 , respectively.
- the transceiver/converter 520 may be part of the Velocity Logic 740 .
- the transceiver/converter 520 may be any device that performs the corresponding functions described.
- the transceiver/converter 520 together with the optical sensors described hereinbefore may use any type of optical grating-based measurement technique, e.g., scanning interferometric, scanning Fabry Perot, acousto-optic-tuned filter (AOTF), optical filter, time-of-flight, etc., having sufficient sensitivity to measure the ac pressures within the pipe, such as that described in one or more of the following references: A.
- phase fractions i.e. the quantity of each phase
- phase flow rates i.e. the speed at which each phase flows in the mixture
- a specific multiphase flow model is not needed for the present invention; any well-known multiphase flow models may be used.
- model itself will be described below in somewhat general terms as the exact methods differ between available models.
- the model itself is not the novel feature of the present invention; instead, it is the incorporation of a fluid sound speed measurement into the model, which provides a more accurate determination of phase flow rates.
- Multiphase flow models incorporating only pressure and temperature measurements have difficulty in predicting phase flow rates. This may largely result from the temperature measurement, because experience has shown that temperature remains difficult to measure accurately. Without accurate measurements the model cannot accurately describe the fluid. Furthermore, if temperature is used in the error function of the flow model (Eq. 22, discussed below), a description of the overall heat transfer characteristics of the well is necessary but, unfortunately, difficult to establish. Another problem appears, which is discussed in detail below, when evaluating the error function of the phase flow rates; namely multiple local minima appear. As one skilled in the art would know, error functions exhibiting many local minima make it difficult to find the true solution. Incorporating fluid sound speed into known multiphase flow models significantly increases the capability of a model to predict phase flow rates.
- FIG. 32 illustrates a single zone application of a multiphase flow measurement system according to the present invention.
- a production pipe 14 extends from the reservoir to the platform 54 .
- a flow meter 1006 is connected to the production pipe 14 approximately 100 meters or further from the wellhead 55 .
- the depth at which gas comes out of solution largely determines this distance, although this distance can vary depending on the application.
- typical hydrocarbon and water mixtures remain in the bubbly flow regime at approximately 15% to 30% gas fraction for mixture flow rates >5 ft/sec in nearly vertical flows and at pressures of greater than approximately 3000 psi.
- the flow meter 1006 consists of two subassemblies, a pressure assembly 1002 and a flow assembly 1004 separated by a short length of pipe called a pup joint 1008 .
- Each assembly has separate fiber optic cables 52 for sending and receiving light to interrogate sensors within the subassemblies.
- the pup joint 1008 measures about 5 to 10 feet in length. It is desired to design the pup joint as short as possible so that the axial location of the pressure assembly 1002 and the flow assembly 1004 is effectively the same for measurement purposes, which is particularly true when one considers that production pipes can reach depths of thousands of feet.
- the pressure assembly 1002 and the flow assembly 1004 each have standard premium thread connectors 1003 to attach to a standard pipe 14 such as 3.5 inch diameter production tubing.
- the pressure assembly 1002 is about 5 feet in length and contains a 15,000-psi pressure and temperature transducer, such as the sensor apparatus disclosed in U.S. Pat. No. 6,016,702, entitled “High Sensitivity Fiber Optic Pressure Sensors For Use In Harsh Environments,” which is incorporated by reference in its entirety.
- the flow assembly 1004 measures about 12 feet in length and contains a fiber optic velocity and a sound speed sensor, such as those described above in detail.
- the diameter of each assembly typically measures 5.60 inches because a protective housing surrounds the sensors, as is known.
- a sensor 1010 located below the choke valve 58 measures wellhead pressure and/or temperature.
- the sensor 1010 may be located on either side or on both sides of the choke valve 58 .
- the sensor 1010 may comprise an electrical strain gauge or an optical fiber sensor.
- the sensor 1010 is located at a spatially removed location from the flow meter 1006 . Locating the sensor 1010 in a vertically removed location from the flow meter 1006 insures that the pressure gradient between the sensor 1010 and the pressure assembly 1002 varies sufficiently in order to calculate a difference in pressure., If the difference in these pressures is negligible, the model may not accurately predict phase flow rates.
- the data from the pressure assembly 1002 and the flow assembly 1004 travels through each fiber optic cable 52 from its respective connector region 1005 to the instrumentation unit 56 .
- Standard clamps 1012 such as LaSalle clamps, secure the cable 52 to the pipe 14 .
- the clamp 1012 may further secure other cable lines such as methanol injection lines and/or a subsurface safety valve lines, or other lines as is known in the art.
- the fiber optic cable 52 may include a protection sheath that surrounds and protects the raw optical fiber within it.
- the instrumentation unit 56 preferably consists of an optical light source, an opto-electronic interrogation unit, a signal demodulation unit, a microprocessor, monitor, keyboard, associated power supplies, disk drives, data communication interfaces, the multiphase flow model 16 software and other necessary items.
- Any type of a multiphase flow model may be used including, but not limited to, flow model software manufactured by ABB Ltd. of Zurich, Switzerland, or Idun software systems from FMC Kongsberg SubSea of Houston, Tex./Kongsberg, Norway.
- the model 16 predicts the phase flow rates in the basic manner depicted by FIG. 33.
- the flow model 16 preferably begins at step 70 where the fluid is defined thermodynamically, such as with a pressure measurement P ref and/or a temperature measurement T ref . However in place of measuring these parameters, they may instead be estimated and entered into the model 16 .
- the pressure assembly 1002 provides P ref and T ref to the instrumentation unit 56 .
- the next step 71 then makes a determination of “slippage” in the fluid. If a fluid has minimal slippage or no slippage, all phases within the fluid are flowing at basically the same rate and the initial estimation of individual phase flow rates is considerably less complicated. Fluid with minimal slippage typically has a high flow rate and occurs in a vertically inclined pipe, which is a typical scenario in an oil/gas well.
- the predicted phase flow rates for a minimal slippage fluid may be calculated from the following:
- phase fractions ⁇ of the fluid mixture possibly cannot be directly determined from the speed of sound sensor, and instead the model makes an iterative determination of the phase fractions.
- phase flow rates for a fluid mixture with minimal slippage is initially determined in step 72 .
- the model will estimate (as opposed to calculate) the initial phase flow rates in step 73 .
- This estimation varies between models, but generally, the basic information of the fluid, pipe geometry, the path fluid travels, constrictions within the pipe, and other factors known in the art are evaluated. As one skilled in the art would realize, the results of a good multiphase flow model do not depend on the accuracy of the predicted phase flow rates. Instead, by the error minimization process described below any predicted flow rate should eventually lead to the true flow rate after several iterations through the error function (Eq. 22 below).
- the model 16 can calculate, in step 74 , any flow-related parameter as long as the proper transfer function is known.
- the model 16 requires at a minimum one measurement for every phase flowing in the fluid 12 in addition to the preferable starting point measurements, i.e. P ref and T ref .
- a two-phase oil/water fluid would require two additional measurements as well as the P ref and/or T ref
- an oil/water/gas fluid requires three additional measurements as well as the P ref and/or T ref .
- the additional measurements include fluid sound speed and at a minimum, either pressure, temperature, velocity or an additional fluid sound speed.
- step 74 sound speed is calculated through known transfer functions, as previously noted, another one or two parameters (depending on the number of phases) such as pressure, temperature and/or velocity is likewise calculated. These calculated parameters are then compared to the corresponding measured parameters as indicated by step 75 .
- the corresponding measurement parameters would include fluid sound speed and velocity from the flow assembly 1004 and wellhead pressure and/or temperature from sensor 1010 . The comparison is then evaluated through an error function in step 76 (Eq. 22) which will be described in more detail below.
- a simplified example may help illustrate the basic method behind multiphase flow models.
- Q is the estimated flow rate of the mixture
- A is the cross sectional area of the pipe
- ⁇ is the density of the fluid mixture which can be measured or estimated by known methods
- k is a known discharge coefficient
- P 1 is the pressure at the starting point, which initially is equal to Pref.
- the model calculates a P 2 at successive intervals until it estimates a pressure drop calculation at the well head 55 , P wh .
- the model compares this estimated P wh with the actual P wh measurement from the pressure sensor 1010 .
- the amount of error between the two results is analyzed by the error function (Eq. 22).
- the result leads the model to choose corresponding phase flow rates (step 77 ) and the process begins again. The process will repeat itself until the error is within acceptable limits and the results are then taken as the true phase flow rates and stored in step 78 .
- Eq. 21 estimates the mixture flow rate Q w , not the individual flow rates, thus one may wonder as to how this equation may help in determining the individual flow rates. What Eq. 21 does provide, however, is an additional constraint to the model, which enables the model to determine the individual component flow rates. It, by itself, would not be sufficient to determine component flow rates, but, in conjunction with the other constraints, such as measured mixture sound speed, it adds yet another constraint into the optimization process and improves the ability of the overall optimization of determining component flow rates.
- the multiphase model couples to an error function to continually narrow the initial estimated phase flow rates to arrive at the correct solution. What has been discovered is that by incorporating fluid sound speed into this standard error function the accuracy of the predicted phase flow rates significantly improves.
- j represents the parameter at issue (e.g. sound speed)
- W is a user defined weight factor for that parameter
- X m and X c are the measured and corresponding calculated parameters respectively.
- FIGS. 34 and 35 represent a fluid with a gas/oil ratio (GOR) of 200 with Fis. 34 representing oil rate (Q o ) and FIG. 35 representing water rate (Q w ).
- GOR gas/oil ratio
- FIG. 35 representing water rate (Q w ).
- the error range of +/ ⁇ 5% is depicted in the graph as two horizontal lines.
- the total liquid flow rate extends along the x-axis with units of Sm 3 /D, which is standard meters 3 per day. One may realize that the graphs show total liquid flow as opposed to the individual phase flow rates.
- the velocity sensor directly measures the total liquid flow measurement, while the model indirectly measures the individual phase flow rates.
- the graphs become easily comparable to each other and the data is plotted by a direct measurement instead of a one step removed, indirect measurement.
- the desired individual phase flow rate Q o , Q w , Q g ) can be determined (taking into consideration the error percentage).
- FIGS. 34 and 35 many points fall outside of the 5% error range.
- FIG. 34 several data points fall outside of the 50% and even 100% error range, clearly indicating how poorly the model predicts oil flow rates with pressure and temperature measurements alone.
- FIG. 35 the data significantly erodes with error percentages approaching 3500%.
- high watercuts such as 60% and 80% have some of the highest errors. As one of skill in the art may realize these watercuts should instead have the greatest accuracy, as will be discussed below.
- FIG. 36 establishing the value of the error function (from Eq. 22) based on one single pass through the search routine generated the data for FIG. 36.
- the error function is graphed for three GORs (150, 200, and 250). Again the total liquid flow rate is on the x-axis, watercut is on the y-axis and the error function is on the z-axis.
- the figure demonstrates that for a model incorporating temperature and pressure measurements alone, multiple local minima 1020 appear for any set of parameters. For example with a GOR of 200, at least four local minima appear, effectively masking the true solution minimum 1022 , which is shown at 4000 Sm 3 /D for a GOR of 200. These local minima 1020 can mislead one to believe that the true minimum 1022 lies within reach, when in fact a local minimum is leading to the wrong result.
- FIGS. 37 - 39 depict a fluid with a GOR of 200. Again two bold lines depict the +/ ⁇ 5% error range and for FIG. 37 (Gas Rate) and FIG. 38 (Oil Rate) nearly every point representing a specific watercut percentage falls within the acceptable range of error.
- the graphs therefore demonstrate the beneficial effect of incorporating speed of sound with velocity and pressure into a multiphase flow model.
- FIG. 40 shows again the improvement of models incorporating sound speed. Once the model has reached the true minimum, the model stores the results in step 78 .
- FIG. 41 there is shown a multizone, multiphase production system 50 having distributed temperature and pressure transducers 32 located at various axial positions along pipe 14 .
- the system 50 further comprises multiple distributed sensor apparatuses 33 located at various axial positions along pipe 14 providing temperature, pressure, speed of sound and/or bulk velocity of the fluid at each location.
- This embodiment has taken FIG. 32 and distributed the basic configuration over many locations. This configuration is more complicated than that described above but derives benefits of combining distributed measurement systems with distributed sound speed and velocity measurements.
- Each sensor produces a signal communicated to the model 16 via cable 52 located at the platform 54 or a remote location.
- it is more difficult, and less meaningful, to attempt to isolate the role of each constraint in the overall optimization system.
- utilizing fully distributed sound speed, velocity, pressure and temperature measurements enables one to address systems of arbitrary complexity. In this optimization, all relationships linking the distributed measurements to the desired quantities can and should be exploited.
- the sensors may comprise any type of sensor capable of measuring the unsteady (or ac or dynamic) pressures within a pipe, such as piezoelectric, optical, capacitive, resistive (e.g., Wheatstone bridge), accelerometers (or geophones), velocity measuring devices, displacement measuring devices, etc.
- the sensors may be Bragg grating based pressure sensors, such as that described in U.S. Pat. No.
- the sensors may be electrical or optical strain gauges attached to or embedded in the outer or inner wall of the pipe and which measure pipe wall strain, including microphones, hydrophones, or any other sensor capable of measuring the unsteady pressures within the pipe.
- the pressure sensors may be connected individually or may be multiplexed along one or more optical fibers using wavelength division multiplexing (WDM), time division multiplexing (TDM), or any other optical multiplexing techniques.
- WDM wavelength division multiplexing
- TDM time division multiplexing
- a portion or all of the fiber between the gratings may be doped with a rare earth dopant (such as erbium) to create a tunable fiber laser, such as is described in U.S. Pat. No. 5,317,576, entitled “Continuously Tunable Single Mode Rare-Earth Doped Laser Arrangement,” to Ball et al., or U.S. Pat. No. 5,513,913, entitled “Active Multipoint Fiber Laser Sensor,” to Ball et al., or U.S. Pat. No. 5,564,832, entitled “Birefringent Active Fiber Laser Sensor,” to Ball et al., all of which are incorporated herein by reference.
- a rare earth dopant such as erbium
- the pressure sensors including electrical strain gauges, optical fibers and/or gratings among others as described, may be attached to the pipe by adhesive, glue, epoxy, tape or other suitable attachment means to ensure suitable contact between the sensor and the pipe.
- the sensors may alternatively be removable or permanently attached via known mechanical techniques such as by mechanical fastener, by a spring loaded arrangement, by clamping, by a clam shell arrangement, by strapping or by other equivalents.
- the strain gauges, including optical fibers and/or gratings may be embedded in a composite pipe. If desired, for certain applications, the gratings may be detached from (or strain or acoustically isolated from) the pipe if desired.
- the present invention allows the speed of sound to be determined in a pipe independent of pipe orientation, i.e., vertical, horizontal, or any other orientation. Also, the invention does not require any disruption to the flow within the pipe (e.g., an orifice or venturi). Further, the invention may use ac (or unsteady or dynamic) pressure measurements as opposed to static (dc) pressure measurements and is therefore less sensitive to static shifts (or errors) in sensing. Furthermore, if harsh environment fiber optic pressure sensors are used to obtain the pressure measurements, such sensors eliminate the need for any electronic components down-hole, thereby improving reliability of the measurement.
- model 16 and/or Logic may be implemented in software (using a microprocessor or computer) and/or firmware, or may be implemented using analog and/or digital hardware, having sufficient memory, interfaces, and capacity to perform the functions described.
Abstract
Description
- This application is a continuation-in-part of U.S. patent application Ser. No. 09/519,785, entitled “Distributed Sound Speed Measurements for Multiphase Flow Measurement,” filed Mar. 7, 2000, to which priority is claimed under 35 U.S.C. §120.
- This application contains subject matter related to that disclosed in U.S. Pat. No. 6,016,702, entitled “High Sensitivity Fiber Optic Pressure Sensors For Use In Harsh Environments”; U.S. Pat. No. 6,354,147, entitled “Fluid Parameter Measurement in Pipes Using Acoustic Pressures”; U.S. patent application Ser. No. 09/740,760, entitled “Apparatus for Sensing Fluid in a Pipe,” filed Nov. 29, 2000; U.S. patent application Ser. No. 09/346,607, entitled “Flow Rate Measurement Using Unsteady Pressures,” filed Jul. 2, 1999; U.S. patent application Ser. No. 09/997,221, entitled “Method And System For Determining The Speed Of Sound In A Fluid Within A Conduit,” filed Nov. 28, 2001; U.S. Provisional Application Serial No. 60/250,997, entitled “Method And System For Determining The Speed Of Sound In A Fluid Within A Conduit,” filed Dec. 4, 2000; and U.S. patent application Ser. No. 09/729,994, entitled “Method And Apparatus For Determining The Flow Velocity Within A Pipe,” filed Dec. 4, 2000 all of which are incorporated herein by reference in their entirety.
- This invention relates to multiphase flow measurement systems to monitor multiphase flow production. More particularly the present invention incorporates sound speed measurements to fundamentally improve the ability of multiphase flow measurement systems to determine phase flow rates of a fluid.
- It is widely recognized that the ability to measure the individual flow rates of oil/water/gas within co-flowing mixtures of these substances has substantial economic value for the oil and gas industry. The industry has been actively developing multiphase flow meters for the past20 years. During this development process, many techniques have been identified, evaluated, refined, and commercialized.
- The numerous approaches to multiphase flow measurement of the prior art can typically be divided into two main categories of multiphase flow meters (MPFM's). The first category seeks to develop instruments to measure the oil/water/gas flow rates based on localized measurement. This is a typical industry approach in which a variety of measurements are made on the oil/gas/water mixture to help determine the flow rates of the individual components. This approach has focused on developing novel and robust instruments designed to provide precise multiphase flow measurements, such as dual-intensity gamma densitomers, microwave meters, capacitance and conductance meters, etc. Typically MPFM's are a collection of several essentially separate, but co-located measurement devices that provide a sufficient number of measurements to uniquely determine the flow rate at the meter location. Prior art multiphase flow meter manufacturers for monitoring hydrocarbon production include Roxar, Framo, and Fluenta, among others. These MPFM's are typically restricted to operate above the well, either on the surface or subsea, for various reasons including reliability in the harsh environment and complications due to the presence of electrical power. Since the MPFM's typically operate at pressures and temperatures determined by production conditions and operators are typically interested in oil and gas production at standard conditions, the flow rates measured at the meter location are translated to standard conditions through fluid properties data (Pressure, Temperature, and Volumetric properties (PVT)).
- The second category of prior art MPFM's provides multiphase flow rate information by utilizing measurements distributed over the production system in conjunction with a mathematical description, or model, of the production system. The mathematical model utilizes multiphase flow models to relate the parameters sought to estimates for the measured parameters. The flow rates are determined by adjusting the multiphase flow rates to minimize the error between the distributed measurements and those predicted by the mathematical model. The type, number, and location of the measurements that enter into this global minimization process to determine flow rates can vary greatly, with cost, reliability and accuracy all entering into determining the optimal system.
- Several prior art MPFM's have been developed utilizing distributed measurements to estimate production flow rates. Owing to the availability and relatively low cost and reliability of conventional pressure and temperature measurements, these systems have typically tended to focus on utilizing only distributed pressure and temperature measurements to determine flow rates. Unfortunately, the physics linking sparse pressure and temperature measurements to flow rates is rather indirect and relies on estimates of several, often ill-defined flow system properties such as viscosity and wall surface roughness. Thus, although it is theoretically possible to determine flow rates from a limited number of pressure and temperature measurements, it is generally difficult for such systems to match the accuracy of a dedicated multiphase flow measurement system as described above.
- The distributed measurement approaches are fundamentally rooted in the relationship between flow rates and pressure and temperature. Specifically, pressure drop in flow within a pipe is due primarily to viscous losses which are related to flow rate, and hydrostatic head changes which are related to changes in density of fluid and hence composition. Axial temperature gradients are primarily governed by the radial heat transfer from the flow within the production tubing into the formation as the flow is produced and is related to the heat capacity of the fluid, heat transfer coefficients, and the flow rate. The pressure drop and temperature losses are used to predict flow rates. The fundamental problem with this approach is that the relationship between flow rate and either of these two parameters is highly uncertain and often must be calibrated or tuned on a case-by-case basis. For instance, it is known that it is extremely difficult to accurately predict pressure drop in multiphase flow.
- It is also recognized that the accuracy of distributed measurement systems utilizing pressure and temperature measurements can be improved utilizing additional phase fraction measurements provided by prior art sensors such as density, dielectric, and sound wave measurements. These phase fraction measurements and/or volumetric flow rate measurements are performed by auxiliary sensors that constrain the global optimization for specific variables at specific locations. In addition to enhancing the overall accuracy and robustness, the auxiliary sensors reduce the need for in-situ tuning of the optimization procedure required to produce accurate results.
- What is needed is a robust and accurate sensor apparatus for providing temperature, pressure and other flow related parameters to multiphase flow models. It is further necessary to provide a sensor that can survive in harsh downhole environments.
- A multiphase flow measurement system is disclosed that incorporates fluid sound speed measurements into a multiphase flow model thereby fundamentally improving the system's ability to determine phase flow rates of a fluid. The distributed system includes at least one flow meter disposed along the pipe, an additional sensor disposed along the pipe spatially removed from the flow meter, and a multiphase flow model that receives the flow related parameters from the flow meter and the additional sensor to calculate the phase flow rates. Depending on production needs and the reservoir dimensions, the distributed system may utilize a plurality of flow meters disposed at several locations along the pipe and may further include a plurality of additional sensors as well. The distributed system preferably uses fiber optic sensors with Bragg gratings. This enables the system to have a high tolerance for long term exposure to harsh temperature environments and also provides the advantage of multiplexing the flow meters and/or sensors together.
- The flow meter provides parameters to the well bore model including pressure, temperature, velocity and sound speed of the fluid. To provide these parameters, the flow meter includes a pressure assembly and a flow assembly, which may be coupled together as a single assembly or separated into two subassemblies. The pressure assembly preferably contains a pressure sensor for measuring the pressure of the fluid and/or a temperature sensor for measuring the temperature of the fluid. The flow assembly preferably contains a fluid sound speed sensor for measuring the fluid sound speed and/or a velocity sensor for measuring the bulk velocity and volumetric flow rate of the fluid.
- The additional sensor, along with the flow meter, provides the necessary parameters for the multiphase flow model to determine phase flow rates. The additional sensor is disposed along the pipe at a location, spatially removed, from the flow meter, preferably vertically removed, for e.g., downstream from the flow meter. The additional sensor may measure temperature, pressure or with a plurality of additional sensors measure both temperature and pressure. This measurement may be taken at the well head of the pipe, and preferably below the main choke valve.
- The measurements from the additional sensor and the flow meter are received by an optimization procedure which seeks to adjust the parameters of a multiphase flow model of the systems such that the error between the measurements recorded by the sensors and those simulated by the model is minimized. The parameters for which the error is minimized yields the desired flow rates. A variety of multiphase flow models may be used to determine the phase flow rates. Models have incorporated pressure and temperature measurements previously; however, the present invention incorporates a fluid sound speed measurement into the model which significantly improves the ability of the model to determine phase flow rates.
- FIG. 1 is a schematic diagram of a prior art multiphase flow meter;
- FIG. 2 is a schematic diagram of a single zone multiphase flow meter in accordance with the present invention;
- FIG. 3 is a schematic block diagram of a sound speed measurement system, in accordance with one aspect of the present invention;
- FIG. 4 is a graph of the magnitude of the fluid sound speed estimate versus an error term over a range of frequencies, in accordance with one aspect of the present invention;
- FIG. 5 is a portion of a logic flow diagram for measuring fluid sound speed, in accordance with one aspect of the present invention;
- FIG. 6 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location separated by a pair of Bragg gratings, in accordance with one aspect of the present invention;
- FIG. 7 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location with a single Bragg grating between each pair of optical wraps, in accordance with one aspect of the present invention;
- FIG. 8 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location without Bragg gratings, in accordance with one aspect of the present invention;
- FIG. 9 is an alternative geometry of an optical wrap of radiator tube geometry, in accordance with one aspect of the present invention;
- FIG. 10 is an alternative geometry of an optical wrap of a race track geometry, in accordance with one aspect of the present invention;
- FIG. 11 is a side view of a pipe having a pair of gratings at each axial sensing location, in accordance with one aspect of the present invention;
- FIG. 12 is a side view of a pipe having a single grating at each axial sensing location, in accordance with one aspect of the present invention;
- FIG. 13 is a schematic block diagram of a sound speed measurement system in an oil or gas well application, using fiber optic sensors, in accordance with one aspect of the present invention;
- FIG. 14 is a graph of fluid sound speed versus the percent water volume fraction for an oil/water mixture, in accordance with one aspect of the present invention;
- FIG. 15 is a continuation of the logic flow diagram of FIG. 5 for measuring fluid sound speed, in accordance with one aspect of the present invention;
- FIG. 16 is a schematic block diagram of a velocity measurement system, in accordance with one aspect of the present invention;
- FIG. 17 is a side view of a pipe having two sensors that measure a vortical pressure in the pipe, as is known in the art;
- FIG. 18 is a graph of two curves, one from each of the two sensors of FIG. 17;
- FIG. 19 is a graph of a cross-correlation between the two curves of FIG. 18;
- FIG. 20 is a graph of power spectral density plotted against frequency for an unsteady acoustic pressure signal Pacoustic and unsteady vortical pressure signal Pvortical, in accordance with one aspect of the present invention;
- FIG. 21 is a graph of power spectrum of two unsteady vortical pressures and the difference between the two pressures, in accordance with one aspect of the present invention;
- FIG. 22 is a graph of a cross-correlation between two of the curves of FIG. 21, in accordance with one aspect of the present invention;
- FIG. 23 is a graph of measured velocity against reference velocity, in accordance with one aspect of the present invention;
- FIG. 24 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location separated by a pair of Bragg gratings, in accordance with one aspect of the present invention;
- FIG. 25 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location with a single Bragg grating between each pair of optical wraps, in accordance with one aspect of the present invention;
- FIG. 26 is a side view of a pipe having optical fiber wrapped around the pipe at each measurement location without Bragg gratings, in accordance with one aspect of the present invention;
- FIG. 27 is an alternative geometry of an optical wrap of a radiator tube geometry, in accordance with one aspect of the present invention;
- FIG. 28 is an alternative geometry of an optical wrap of a race track geometry, in accordance with one aspect of the present invention;
- FIG. 29 is a side view of a pipe having a pair of gratings at each axial sensing location, in accordance with one aspect of the present invention;
- FIG. 30 is a side view of a pipe having a single grating at each axial sensing location, in accordance with one aspect of the present invention;
- FIG. 31 is a schematic block diagram of a velocity measurement system in an oil or gas well application, using fiber optic sensors, in accordance with one aspect of the present invention;
- FIG. 32 is a representation of a single zone multiphase flow system in accordance with the present invention;
- FIG. 33 is a block diagram of a multiphase flow model in accordance with the present invention;
- FIG. 34 is a graph representing a numerical test of a multiphase flow model incorporating pressure and temperature measurements to determine Oil Rate;
- FIG. 35 is a graph representing a numerical test of a multiphase flow model incorporating pressure and temperature measurements to determine Water Rate;
- FIG. 36 is a graph of the error function created for a multiphase flow model incorporating pressure and temperature measurements to determine phase flow rates;
- FIG. 37 is a graph representing a numerical test of a multiphase flow model incorporating sound speed, velocity and pressure measurements to determine Gas Rate;
- FIG. 38 is a graph representing a numerical test of a multiphase flow model incorporating sound speed, velocity and pressure measurements to determine Oil Rate;
- FIG. 39 is a graph representing a numerical test of a multiphase flow model incorporating sound speed, velocity and pressure measurements to determine Water Rate;
- FIG. 40 is a graph of the error function created for a multiphase flow model incorporating sound speed, velocity and pressure measurements to determine phase flow rates; and
- FIG. 41 is a graphical representation of a multizone multiphase flow system in accordance with the present invention.
- Referring to FIG. 1 there is shown a
prior art MPFM 10 for monitoring flow rates of a multi-phase fluid represented byarrow 12 flowing within apipe 14.Math model 16 of MPFM 10 utilizes output fromsensor 18 and atleast sensor 20 to predict the phase fraction flow rate offluid 12.Sensors model 16 such as temperature, pressure, and phase fraction.Model 16 utilizes the output ofsensors - Referring to FIG. 2 there is shown a
MPFM 30 of the present invention, which utilizessensor 32 andsensor 34.Sensor 32 andsensor 34 may comprise a single sensor or a sensor system comprising multiple sensors or sensor arrays.Sensors multi-phase fluid 12 tosystem model 16. One sensor system, referred to as a “flow meter,” that can be used to measure these parameters is disclosed in U.S. application Ser. No. 09/740,760, entitled “Apparatus for Sensing Fluid in a Pipe,” filed Nov. 29, 2000, which is incorporated herein by reference in its entirety. This particular flow meter combines a fluid sound speed sensor with a velocity sensor.Model 16 utilizes the speed of sound and/or bulk velocity information to provide a robust and accurate multi-phase flow rate Qw to monitor multiphase flow production. Because the present invention preferably employs a fluid sound speed and fluid velocity, the methods for determining these parameters are disclosed in detail in the following sections. - I. Sound Speed Measurements
- A. Basic Considerations To provide fluid sound speed measurements to model16, the present invention utilizes
acoustic sensors fluid 12. The invention preferably uses acoustic signals having lower frequencies (and thus longer wavelengths) than those used for ultrasonic meters, such as below about 20 kHz (depending on pipe diameter). Typically, for 3-7 inch production tubing, the desired frequency range is between 100-2000 hz. As such, the invention is more tolerant to the introduction of gas, sand, slugs, or other inhomogeneities in the fluid. As one skilled in the art would realize, the embodiment described below may also be referred to as a phase fraction meter or sound speed meter. - FIG. 3 discloses a speed of sound meter that could be used for either of the
sensors unsteady pressure sensors pipe 14. Thesensors lines logics lines - The frequency signals P1(ω), P2(ω), P3(ω) are fed to an amix-Mx Calculation Logic 140 which provides a signal on a
line 146 indicative of the speed of sound of the mixture amix. The amix signal is provided to map (or equation)logic 148, which converts amix to a percent composition of the fluid and provides a “% Comp” signal online 150. Also, if the Mach number, Mx, is not negligible and is desired to be known, thecalculation logic 140 may also provide a signal Mx on aline 159 indicative of the Mach number (as discussed below). - For planar one-dimensional acoustic waves in a homogenous mixture, it is known that the acoustic pressure field P(x,t) at a location x along a pipe, where the wavelength λof the acoustic waves to be measured is long compared to the diameter d of the pipe14 (i.e., λ/d>>1), may be expressed as a superposition of a right traveling wave and a left traveling wave, as follows:
- P(x,t)=(Ae −ik r x +Be +ik l x)eiωt Eq. 1
-
-
- where Vmix is the axial velocity of the mixture. For non-homogenous mixtures, the axial Mach number represents the average velocity of the mixture and the low frequency acoustic field description remains substantially unaltered.
- The frequency domain representation P(x,ω) of the time-based acoustic pressure field P(x,t) within a pipe, is the coefficient of the eiωt term of Eq. 1:
- P(x,ω)=Ae−k r x +Be +ik l x Eq. 4
- Referring to FIG. 3, it has been determined that using Eq. 4 at three axially distributed pressure measurement locations x1, x2, X3 along the
pipe 14 leads to an equation for amix as a function of the ratio of frequency based pressure measurements, which allows the coefficients A and B to be eliminated. For optimal results, A and B are substantially constant over the measurement time and substantially no sound (or acoustic energy) is created or destroyed in the measurement section. The acoustic excitation enters the test section only through the ends of thetest section 151 and, thus, the speed of sound within thetest section 151 can be measured independent of the acoustic environment outside of the test section. In particular, the frequency domain pressure measurements P1(ω), P2(ω), P3(ω) at the three locations x1, x2, X3, respectively, along thepipe 14 using Eq. 1 for right and left traveling waves are as follows: - P 1(ω)=P(x=x 1,ω)=Ae −ik r x 1 +Be +Ik l x 1 Eq. 5
- P 2(ω)=P(x=x 2,ω)=Ae −ik r x 2 +Be +ik l x 2 Eq. 6
- P 3(ω)=P(x=x 3,ω)=Ae −ik r x 3 +Be +ik l x 3 Eq. 7
-
- where R is defined as the reflection coefficient.
-
-
- By implementing various equations above, the speed of sound in the fluid may be computed by either: (1) varying amix while minimizing an error term, (2) calculating a logarithmic relationship between the acoustic pressure variation signals, or (3) calculating a trigonometric relationship between the acoustic pressure variation signals.
- B. Determining Speed of Sound (amix by Minimizing an Error Term
-
- and the distinction between the wave numbers for the right and left traveling waves are eliminated. In that case (where Mx is negligible), because all of the variables in Eq. 10 are known except for amix, the value for amix can be iteratively determined by evaluating the error term at a given frequency ω and varying amix until the error term goes to zero. The value of amix at which the magnitude of the error term equals zero (or is a minimum), corresponds to the correct value of the speed of sound in the mixture amix. As Eq. 10 is a function of frequency ω, the speed of sound amix at which the error goes to zero is the same for each frequency ω evaluated. Furthermore, since each frequency is an independent measurement of the same parameter, the multiple measurements may be weighted, averaged or filtered to provide a single more robust measurement of the speed of sound in the fluid.
- Referring to FIG. 4, the error term of Eq. 10 constitutes a family of curves, one curve for each frequency ω, where the value of the error is evaluated for values of amixvaried from awater (5,000 ft/sec) to aoil (4,000 ft/sec) at each frequency varied from 5 to 200 Hz in 5 Hz increments. Other frequencies may be used if desired. The speed of sound amix where the error goes to zero (or is minimized) is the same for each frequency ω evaluated. In this case, the error is minimized at a point 170 when amix is 4335 ft/sec.
- C. Determining Speed of Sound (amix) Using a Logarithmic Relationship
-
-
- where P12=P1(ω/P2(ω), P13=P1(ω)/P3(ω), i is the square root of 1. Because the result of the Log function is also an imaginary number, a real number for the speed of sound amixis yielded.
- The analytical solution to Eq. 10 as reflected in Eqs. 12 and 13 is valid primarily for the frequencies for which the length of the
test section 151 along the pipe 14 (i.e., x3−x1 or 2Δx for equally spaced sensors) is shorter than the wavelength λ of the acoustic waves to be measured. This restriction results because of the multiple possible solutions for Eq. 10. Alternative solutions to Eq. 10 for other frequency ranges may be derived using a variety of known techniques. - D. Determining Speed of Sound (amix) Using a Trigonometric Relationship
-
- Eq. 14 is particularly useful due to its simple geometric form, from which amix can be easily interpreted. In particular, amix can be determined directly by inspection from a digital signal analyzer (or other similar instrument) set up to provide a display indicative of the left side of Eq. 14, which will be a cosine curve from which amix may be readily obtained. For example, at the zero crossing of the cosine wave, amix will be equal to 2ωΔX/π. Alternatively, Eq. 14 may be used to determine amix using an iterative approach where a measured function is calculated from the left side of Eq. 14 (using the measured pressures), which is compared to a cosine curve of the right side of Eq. 14, where amix is varied until it substantially matches the measured function. Various other curve fitting, parameter identification, and/or minimum error or solution techniques may be used to determine the value of amix that provides the best fit to satisfy Eq. 14.
-
- E. Fluid Sound Speed Calculation Logic
- Referring to FIG. 5, the calculation logic140 (see FIG. 3) begins at
step 200 where P12 is calculated as the ratio of P1(ω)/P2(ω), and atstep 202 where P13 is calculated as the ratio of P1(ω)/P3(ω). Next,step 203 determines whether the Mach number Mx of the mixture is negligible (or whether it is desirable to calculate Mx, i.e. for cases where Mx is not negligible, as set forth below with reference to “A” and FIG. 15). If Mx is negligible,step 204 determines if thesensors step 208 calculates amix(n) from the closed form solution of Eq. 13. Then, step 210 checks whether thelogic 140 has calculated amix at a predetermined number of frequencies, e.g., 10. If n is not greater than 10,steps logic 140 has calculated amix at 10 frequencies,logic 140 goes to step 216, which determines an average value for amix using the values of amix(n) over the 10 frequencies, and thelogic 140 then exits. - If the sensors are not equally spaced, a series of
steps 250 are performed starting withstep 220, which sets x1, x2, and X3 to the current pressure sensor spacing, and sets initial values for ω=ω1 (e.g., 100 Hz) and the counter n=1. Next, step 222 sets amix=amix-min (e.g., aoil=4000 ft/sec) and step 224 calculates the error term from Eq. 10. Then, step 226 checks whether error=0. If the error does not equal zero, amix is incremented by a predetermined amount and thelogic 140 goes to step 224. - If the error=0 (or a minimum) in
step 226, step 230 sets amix(n)=amix. Next, step 232 checks whether n is greater than or equal to 10. If not, step 234 increments n by one and step 236 increases the frequency ω by a predetermined amount (e.g., 10 Hz) and continues atstep 222 as shown in FIG. 15. If n is greater than or equal to 10, step 238 calculates an average value for amix over the 10 frequencies, and thelogic 140 ends. - Referring to FIG. 15, if the Mach number Mx is not negligible,
several steps step 306. If the result ofstep 310 is yes, step 314 increases Mx by a predetermined amount (e.g., 1) and the logic goes back tostep 304. - When
step 308 indicates error=0 (or a minimum),step 316 sets amix(n)=amix and Mx(n)=Mx, and step 318 checks whether the values of amix and Mx have been calculated at 10 different frequencies. If not, step 320 increments the counter n by one and step 322 increases the value of the frequency ω by a predetermined amount (e.g., 10 Hz), and the logic goes back tostep 302. If the values of amix and Mx have been calculated at 10 different frequencies (i.e., n is equal to 10),step 324 calculates average values for amix(n) and Mx(n) at the 10 different frequencies to calculate amix and Mx, and the logic exists. - F. Fiber Optic Embodiments
- Referring to FIG. 6, for embodiments of the present invention utilizing fiber optic sensors with the
wraps fiber 400 at opposite ends of each of thewraps gratings wrap 402 may have a common reflection wavelength λ1, and the second pair ofgratings wrap 404 may have a common reflection wavelength λ2, but different from that of the first pair ofgratings gratings wrap 406 have a common reflection wavelength λ3, which is different from λ1 and λ2. Thefiber 400 may continue to other sensors as shown byreference numeral 17 or return the optical signals to the instrument as shown byreference numeral 15. - Referring to FIG. 7, instead of having a different pair of reflection wavelengths associated with each wrap, a series of
Bragg gratings wraps - Referring to FIGS. 6 and 7, the
wraps gratings gratings fiber 400 and a series of optical pulses are reflected back along thefiber 400. The length of each wrap can then be determined by the time delay between each return pulse. - While the gratings are shown oriented axially with respect to
pipe 14 in FIGS. 6 and 7, the gratings may be oriented along thepipe 14 axially, circumferentially, or in any other orientations. Depending on the orientation, the grating may measure deformations in the pipe wall with varying levels of sensitivity. If the grating reflection wavelength varies with internal pressure changes, such variation may be desired for certain configurations (e.g., fiber lasers) or may be compensated for in the optical instrumentation for other configurations, e.g., by allowing for a predetermined range in reflection wavelength shift for each pair of gratings. Alternatively, instead of each of the wraps being connected in series, they may be connected in parallel, e.g., by using optical couplers (not shown) prior to each of the wraps, each coupled to thecommon fiber 400. - Referring to FIG. 8, alternatively, the
sensors pipe 14 with thewraps separate fibers corresponding wraps pipe 14 due to pressure changes within the pipe. These known interferometric techniques include the Mach Zehnder or Michaelson Interferometric techniques that are described in U.S. Pat. No. 5,218,197, entitled “Method And Apparatus For The Non-Invasive Measurement Of Pressure Inside Pipes Using A Fiber Optic Interferometer Sensor,” to Carroll. The inteferometric wraps may also be multiplexed as described in Dandridge, et al., “Fiber Optic Sensors for Navy Applications,” IEEE, February 1991, or Dandridge, et al., “Multiplexed Interferometric Fiber Sensor Arrays,” SPIE, Vol. 1586, 1991, pp. 176-183. Other techniques to determine the change in fiber length may also be used. Also, reference optical coils (not shown) may be used for certain interferometric approaches and may also be located on or around thepipe 14 but may be designed to be insensitive to pressure variations. - Referring to FIGS. 9 and 10, instead of the
wraps pipe 14, thewraps pipe 14 is cut axially and laid flat. In this particular embodiment, thewraps pipe 14 with a length long enough to optically detect the changes to the pipe circumference. Other geometries for the wraps may be used if desired. Also, for any geometry of the wraps described, more than one layer of fiber may be used depending on the overall fiber length desired. The desired axial length of any particular wrap is set depending on the characteristics of the ac pressure desired to be measured, for example the axial length of the pressure disturbance caused by a vortex to be measured. - Referring to FIGS. 11 and 12, embodiments of the present invention include configurations wherein instead of using the
wraps fiber 400 may have shorter sections that are disposed around at least a portion of the circumference of thepipe 14 that can optically detect changes to the pipe circumference. It is further within the scope of the present invention that sensors may comprise anoptical fiber 400 disposed in a helical pattern (not shown) aboutpipe 14. As discussed above, the orientation of the strain sensing element will vary the sensitivity to deflections in pipe wall deformations caused by unsteady pressure signals in thepipe 14. - FIG. 13 illustrates an embodiment of a sound speed measurement system in an oil or gas well application. The
sensing section 151 may be connected to or part of the production tubing 602 (analogous to thepipe 14 in the test section 151) within a well 600. Anisolation sleeve 510 may be located over thesensors pipe 602 at its axial ends to protect thesensors sensors pipe 602, and/or to help isolate ac pressures in thepipe 602 from ac pressures outside thepipe 602. Thesensors cable 606 which may comprise anoptical fiber 400 and is connected to a transceiver/converter 610 located outside thewell 600. - When optical sensors are used, the transceiver/
converter 610 may be used to receive and transmitoptical signals 604 to thesensors sensors lines converter 610 may be part of theFluid Parameter Logic 160. The transceiver/converter 610 may be any device that performs the corresponding functions described. In particular, the transceiver/converter 610 together with the optical sensors described above may use any type of optical grating-based measurement technique, e.g., scanning interferometric, scanning Fabry Perot, acousto-optic-tuned filter (AOTF), optical filter, time-of-flight, and may use WDM and/or TDM, etc., having sufficient sensitivity to measure the ac pressures within the pipe, such as that described in one or more of the following references: A. Kersey et al., “Multiplexed fiber Bragg grating strain-sensor system with a Fabry-Perot wavelength filter,” Opt. Letters, Vol. 18, No. 16, August 1993; U.S. Pat. No. 5,493,390, issued Feb. 20, 1996, to Mauro Verasi, et al.; U.S. Pat. No. 5,317,576, issued May 31, 1994, to Ball et al.; U.S. Pat. No. 5,564,832, issued Oct. 15, 1996, to Ball et al.; U.S. Pat. No. 5,513,913, issued May 7, 1996 to Ball et al.; U.S. Pat. No. 5,426,297, issued Jun. 20, 1995, to Dunphy et al.; U.S. Pat. No. 5,401,956, issued Mar. 28, 1995, to Dunphy et al.; U.S. Pat. No. 4,950,883, issued Aug. 21, 1990, to Glenn; and U.S. Pat. No. 4,996,419, issued Feb. 26, 1991 to Morey, all of which are incorporated by reference. Also, the pressure sensors described may operate using one or more of the techniques described in the aforementioned references. - G. Determining Phase Fraction From The Measured Sound Speed
- Turning back to FIG. 2, in particular,
sensors - ρmix=ρoilφoil+Pwφw+Pgasφgas Eq. 16
-
- Where ρ is the density of the mix or constituent of the multi-component mixture, a is the sound speed of the mix or constituent of the mixture, and φ is the volumetric phase fraction of the mix or constituent of the mixture. Thus, knowledge of the sound speed and densities of the oil, water, and gas components provide a relation between the sound speed of the mixture and the in-situ phase fraction of the fluids.
- Referring to FIG. 14, where the fluid is an oil/water mixture, a
curve 110 shows the speed of sound in the mixture amix plotted as a function of water volume fraction. For this illustrative example, the values used for density (p) and speed of sound (a) in oil and water are as follows: - Density (ρ): ρwater=1,000 kg/m3; ρoil=700 kg/m3
- Speed of sound (a): awater=5,000 ft/sec; aoil=4,000 ft/sec.
- It should be understood that the present invention can be used to measure fluid volume fractions of a mixture of any number of fluids in which the speed of sound of the mixture amix is related to (or is substantially determined by) the volume fractions of two constituents of the mixture, e.g., oil/water, oil/gas, water/gas. The present invention can be used to measure the speed of sound of any mixture and can then be used in combination with other known quantities to derive phase content of mixtures with multiple (more than two) constituents.
- H. Other Sound Speed Measurement Techniques
- U.S. patent application Ser. No. 09/997,221, entitled “Method And System For Determining The Speed Of Sound In A Fluid Within A Conduit,” filed Nov. 28, 2001, which claims priority to U.S. Provisional Application Serial No. 60/250,997, entitled “Method And System For Determining The Speed Of Sound In A Fluid Within A Conduit,” filed Dec. 4, 2000, both disclose an alternative method for determining the speed of sound of a fluid within a pipe, and both are incorporated herein by reference in their entireties.
- II. Bulk Velocity Measurements
- A. Basic Considerations
- The present invention further includes
velocity sensors determination utilizing model 16. For well-mixed flows offluid 12 within apipe 14, ahomogeneous model 16 which assumes that all the phases are flowing at the same velocity may be sufficient. In other cases, slip models may be required to translate flow velocities provided from cross correlation measurements into individual component flow rates. In either case, the present invention incorporates cross correlation measurements that improve the predictive performance of themodel 16 for multi-phase flow Qw information. As described below, the sensors provide bulk velocity measurement to model 16 (FIG. 2) by measuring vortical pressures in the fluid. As one skilled in the art would recognize the embodiment described below may be referred to as a flow meter. - Referring to FIG. 16, a velocity and flow measurement system includes a
sensing section 710 along a pipe, or conduit, 14 and avelocity logic section 740. Thepipe 14 has twomeasurement regions pipe 14. At thefirst measurement region 714 are two unsteady (or dynamic or ac)pressure sensors pipe 14, and at thesecond measurement region 716, are two otherunsteady pressure sensors pipe 14. Each pair ofpressure sensors - The
flow measurement system 710 of the present invention measures velocities associated with unsteady flow fields and/or pressure disturbances represented by 715 such as turbulent eddies (or vortical flow fields), inhomogeneities in the flow (such as bubbles, slugs, and the like), or any other properties of the flow, fluid, or pressure, having time varying or stochastic properties in the form of unsteady pressures. The vortical flow fields 715 are, in general, comprised of pressure disturbances having a wide variation in length scales and which have a variety of coherence length scales such as that described in the reference “Sound and Sources of Sound,” A. P. Dowling et al, Halsted Press, 1983. Vortical flow fields often convect at or near the mean velocity of at least one of the fluids within a mixture flowing in a pipe. More specifically, the vortices convect in a predictable manner with reference to the fluids. Thevortical pressure disturbances 715 that contain information regarding convection velocity have temporal and spatial length scales as well as coherence length scales that differ from other disturbances in the flow. The present invention utilizes these properties to preferentially select disturbances of a desired axial length scale and coherence length scale as will be more fully described hereinafter. For illustrative purposes, the terms vortical flow field and vortical pressure field will be used to describe the above-described group of unsteady pressure fields having temporal and spatial length and coherence scales described. - The pressures P1, P2, P3, P4 may be measured through holes in the
pipe 14 ported to external pressure sensors or by other techniques discussed hereinafter. Thepressure sensors lines Velocity Logic 740 which provides a convection velocity signal Uc(t) on aline 742 which is related to an average flow rate Uf(t) of the fluid flowing in the pipe 14 (where fluid may comprise one or more liquids and/or gases; where the gas(es) may be dissolved in the liquid or in free gas form, and wherein the fluid may include non-liquid elements). - In particular, in the
Velocity Logic 740, the pressure signal P1(t) on theline 730 is provided to a positive input of asummer 744 and the pressure signal P2(t) on theline 732 is provided to a negative input of thesummer 744. The output of thesummer 744 is provided on aline 745 indicative of the difference between the two pressure signals P1, P2 (e.g., P1−P2=Pas1). - The
pressure sensors summer 744 create aspatial filter 733. Theline 745 is fed tobandpass filter 746, which passes a predetermined passband of frequencies and attenuates frequencies outside the passband. In accordance with the present invention, the passband of thefilter 746 is set to filter out (or attenuate) the dc portion and the high frequency portion of the input signals and to pass the frequencies therebetween. For example, in a particular embodimentbandpass filter 746 is set to pass frequencies from about 1 Hz to about 100 Hz, for a 3 inch ID pipe flowing water at 10 ft/sec. Other passbands may be used in other embodiments, if desired.Bandpass filter 746 provides a filtered signal Pasf1 on aline 748 toCross-Correlation Logic 750, described below. - The pressure signal P3(t) on the
line 734 is provided to a positive input of asummer 754 and the pressure signal P4(t) on theline 736 is provided to a negative input of thesummer 754. Thepressure sensors summer 754 create aspatial filter 735. The output of thesummer 754 is provided on aline 755 indicative of the difference between the two pressure signals P3, P4 (e.g., P3−P4=Pas2). Theline 755 is fed to abandpass filter 756, similar to thebandpass filter 746 discussed hereinbefore, which passes frequencies within the passband and attenuates frequencies outside the passband. Thefilter 756 provides a filtered signal Pasf2 on aline 758 to theCross-Correlation Logic 750. The signs on thesummers summers summers - The
Cross-Correlation Logic 750 calculates a known time domain cross-correlation between the signals Pasf1 and Pasf2 on thelines line 760 indicative of the time delay T it takes for an vortical flow field 715 (or vortex, stochastic, or vortical structure, field, disturbance or perturbation within the flow) to propagate from onesensing region 714 to theother sensing region 716. Such vortical flow disturbances, as is known, are coherent dynamic conditions that can occur in the flow which substantially decay (by a predetermined amount) over a predetermined distance (or coherence length) and convect (or flow) at or near the average velocity of the fluid flow. As described above, thevortical flow field 715 also has a stochastic or vortical pressure disturbance associated with it. In general, thevortical flow disturbances 715 are distributed throughout the flow, particularly in high shear regions, such as boundary layers (e.g., along the inner wall of the pipe 14) and are shown as discrete vortical flow fields 715. Because the vortical flow fields 715 (and the associated pressure disturbance) convect at or near the mean flow velocity, the propagation time delay T is related to the velocity of the flow by the distance ΔX between themeasurement regions - A spacing signal ΔX on a
line 762 indicative of the distance ΔX between thesensing regions line 760 by adivider 764 which provides an output signal on theline 742 indicative of the convection velocity Uc(t) of the fluid flowing in thepipe 14, which is related to (or proportional to or approximately equal to) the average (or mean) flow velocity Uf(t) of the fluid, as defined below: - U c(t)=ΔX/τ∝U f(t) Eq. 18
- The convection velocity Uc(t) may then be calibrated to more precisely determine the mean velocity Uf(t) if desired. The result of such calibration may require multiplying the value of the convection velocity Uc(t) by a calibration constant (gain) and/or adding a calibration offset to obtain the mean flow velocity Uf(t) with the desired accuracy. For some applications, such calibration may not be required to meet the desired accuracy. The velocities Uf(t), Uc(t) may be converted to volumetric flow rate by multiplying the velocity by the cross-sectional area of the pipe.
- Referring to FIGS. 17, 18,19 as is known, cross-correlation may be used to determine the time delay τ between two signals y1(t), y2(t) separated by a known distance ΔX, that are indicative of
quantities 780 that convect with the flow (e.g., density perturbations, concentration perturbations, temperature perturbations, vortical pressure disturbances, and other quantities). In FIG. 18, the signal y2(t) lags behind the signal y1(t) by 0.15 seconds. If a time domain cross-correlation is taken between the two signals y1(t), y2(t), the result is shown in FIG. 19 as acurve 784. Thehighest peak 786 of thecurve 784 shows the best fit for the time lag τ between the two signals y1(t), y2(t) is at 0.15 seconds which matches the reference time delay shown in FIG. 18. - Referring to FIG. 16, as discussed hereinbefore, since pressure disturbances associated within the
vortical flow field 715 convect (or flow) at or near the average velocity of the fluid flowing in thepipe 14, the vortical pressure disturbances observed at thedownstream location 716 are substantially a time lagged version of the vortical pressure disturbances observed at theupstream location 714. However, the total vortical pressure perturbations or disturbances in a pipe may be expressed as being comprised of vortical pressure disturbances (Pvortical), acoustic pressure disturbances (Pacoustic) and other types of pressure disturbances (Pother) as shown below expressed in terms of axial position along the pipe at any point in time: - P(x,t)=P vortical(x,t)+P acoustic(x,t)+Pother(x,t) Eq. 19
- As a result, the unsteady pressure disturbances Pvortical can be masked by the acoustic pressure disturbances Pacoustic and the other types of pressure disturbances Pother. In particular, the presence of the acoustic pressure disturbances that propagate both upstream and downstream at the speed of sound in the fluid (sonic velocity), can prohibit the direct measurement of velocity from cross-correlation of direct vortical pressure measurements.
- The present invention uses temporal and spatial filtering to precondition the pressure signals to effectively filter out the acoustic pressure disturbances Pacoustic and other long wavelength (compared to the sensor spacing) pressure disturbances in the
pipe 14 at the twosensing regions vortical flow field 715 and any other short wavelength (compared to the sensor spacing) low frequency pressure disturbances Pother. In accordance with the present invention, if the low frequency pressure disturbances Pother are small, they will not substantially impair the measurement accuracy of Pvortical. - The Pvortical dominated signals from the two
regions locations sensing region 714, the difference between the twopressure sensors spatial filter 733 that effectively filters out (or attenuates) acoustic disturbances for which the wavelength λ of the acoustic waves propagating along the fluid is long (e.g., ten-to-one) compared to the spacing X1 between the sensors. Likewise the same is true forspatial filter 735. Other wavelength to sensor spacing ratios may be used to characterize the filtering, provided the wavelength to sensor spacing ratio is sufficient to satisfy the two-to-one spatial aliasing Nyquist criteria. - Referring to FIG. 20, relevant features of the power spectral density (PSD) of typical vortical pressure disturbances PVortical is shown by a
curve 790 that has a flat region (or bandwidth) up to a frequency Fv and then decreases with increasing frequency f. The value of Fv is approximately equal to U/r, where U is the flow rate and r is the radius of the pipe. For example, for a flow rate U of about 10 ft/sec and a pipe radius r of about 0.125 ft (or about 1.5 inches), the bandwidth Fv of the vortical pressure disturbances Pvortical would be about 80 Hz (10/0.125). The PSD of the acoustic pressure disturbances Pacoustic has a profile that is determined by the environment and other factors and is indicated in the figure by anarbitrary curve 791, and typically has both low and high frequency components. - The acoustic
spatial filters 733, 735 (FIG. 16) discussed hereinbefore block or attenuate wavelengths longer than λas and frequencies below fas, as indicated by the region 796. Also, the bandpass filters (BPF) 746, 756 (FIG. 16) block or attenuate high frequencies above fpb having short and long wavelengths and pass frequencies below fas where the Pvortical signals exist. Thus, after thespatial filters lines 748, 758 (FIG. 16) will be dominated by the short wavelength unsteady pressure disturbances PVortical at frequencies below fpb and as indicated by aportion 794 of thecurve 790 in the BPF passband 795 (FIG. 20). - Accordingly, referring to FIG. 20, the
spatial filters 733, 735 (FIG. 16) block the long wavelengths, which, for the acoustic pressure disturbances Pacoustic, occur at low frequencies as indicated to the left of a dashedline 792 at frequencies below the frequency fas. A dashedline 793 indicates the attenuation of the acoustic pressure Pacoustic signal 791 below the frequency fas at the output of the spatial filters. The vortical pressure disturbances Pvortical are substantially not attenuated (or only slightly attenuated) because Pvortical has short wavelengths at low frequencies that are substantially passed by the spatial filter. The BPF's 746, 756 (FIG. 16) block or attenuate frequencies outside the passband indicated by a range offrequencies 795, and passes the unsteady pressure disturbances associated with stochastic flow fields 715 (FIG. 16) within thepassband 795. - Alternatively, instead of the
filters filters filters frequencies 789. It should be understood that thefilters - Referring to FIGS. 21 and 16, for the four
ac pressure sensors pipe 14, and providing ac pressure signals P1, P2, P3, P4, respectively, the frequency power spectrum for P1 and P2 are shown bycurves inch diameter schedule 780 pipe using conventional piezoelectric ac pressure transducers. The power spectra of thecurves curve 804 is reduced in certain frequency bands (e.g., 100-150 Hz) and increased in other frequency bands (e.g., 200-250 Hz) as compared to theindividual signals - Referring to FIGS. 22 and 16, the cross correlation between the signals Pas1 (or P1−P2) and Pas2 (P3−P4) is shown as a
curve 810. Thehighest peak 812 indicates the best fit for the time lag between the two signals Pas1, Pas2 as 0.015 seconds. Because the four sensors P1 to P4 were evenly axially spaced 1 inch apart, the effective distance ΔX between the sensor pairs is 2 inches. Thus, the velocity measured from Eq. 18 is 11.1 ft/sec (2/12/0.015) using the present invention and the actual velocity was 11.2 ft/sec. - Referring to FIG. 23, for the configuration described with FIGS. 16, 21,22 above, the velocity was measured at various flow rates and plotted against a reference velocity value. A
solid line 820 shows the reference velocity, thetriangles 822 are the measured data, and aline 824 is a curve fit of thedata 822. This illustrates that the present invention predicts the flow velocity within a pipe (or conduit). - B. Fiber Optic Embodiments For Velocity Sensors
- Referring to FIGS. 24, 25,26 if an optical strain gage is used, the ac pressure sensors 718-724 may be configured using an
optical fiber 900 that is coiled or wrapped around and attached to thepipe 14 at each of the pressure sensor locations as indicated by the coils or wraps 902, 904, 906, 908 for the pressures P1, P2, P3, P4, respectively. The fiber wraps 902-908 are wrapped around thepipe 14 such that the length of each of the fiber wraps 902-908 changes with changes in the pipe loop strain in response to unsteady pressure variations within thepipe 14 and thus internal pipe pressure is measured at the respective axial location. Such fiber length changes are measured using known optical measurement techniques as discussed hereinafter. Each of the wraps measures substantially the circumferentially averaged pressure within thepipe 14 at a corresponding axial location on thepipe 14. Also, the wraps provide axially averaged pressure over the axial length of a given wrap. While the structure of thepipe 14 provides some spatial filtering of short wavelength disturbances, we have found that the basic principle of operation of the invention remains substantially the same as that for the point sensors described previously. - Referring to FIG. 24, for embodiments of the present invention where the
wraps fiber 900 at opposite ends of each of thewraps gratings wrap 902 may have a common reflection wavelength λ1, and the second pair ofgratings wrap 904 may have a common reflection wavelength λ2, but different from that of the first pair ofgratings gratings wrap 906 have a common reflection wavelength λ3, which is different from λ1, λ2, and the fourth pair ofgratings wrap 908 have a common reflection wavelength λ4, which is different from λ1, λ2, λ3. Thefiber 400 may continue to other sensors as shown byreference numeral 17 or return the optical signals to the instrument as shown byreference numeral 15. - Referring to FIG. 25, instead of having a different pair of reflection wavelengths associated with each wrap, a series of Bragg gratings960-968 with only one grating between each of the wraps 902-908 may be used each having a common reflection wavelength λ1.
- Referring to FIGS. 24 and 25 the wraps902-908 with the gratings 910-924 (FIG. 24) or with the gratings 960-968 (FIG. 25) may be configured in numerous known ways to precisely measure the fiber length or change in fiber length, such as an interferometric, Fabry Perot, time-of-flight, or other known arrangements. An example of a Fabry Perot technique is described in U.S. Pat. No. 4,950,883, entitled “Fiber Optic Sensor Arrangement Having Reflective Gratings Responsive to Particular Wavelengths,” to Glenn. One example of time-of-flight (or Time-Division-Multiplexing; TDM) would be where an optical pulse having a wavelength is launched down the
fiber 900 and a series of optical pulses are reflected back along thefiber 900. The length of each wrap can then be determined by the time delay between each return pulse. - While the gratings910-924 are shown oriented axially with respect to the
pipe 14, in FIGS. 24 and 25, they may be oriented along thepipe 14 axially, circumferentially, or in any other orientations. Depending on the orientation, the grating may measure deformations in the pipe wall 952 with varying levels of sensitivity. If the grating reflection wavelength varies with internal pressure changes, such variation may be desired for certain configurations (e.g., fiber lasers) or may be compensated for in the optical instrumentation for other configurations, e.g., by allowing for a predetermined range in reflection wavelength shift for each pair of gratings. Alternatively, instead of each of the wraps being connected in series, they may be connected in parallel, e.g., by using optical couplers (not shown) prior to each of the wraps, each coupled to thecommon fiber 900. - Referring to FIG. 26, alternatively, the sensors718-724 may also be formed as individual non-multiplexed interferometric sensor by wrapping the
pipe 14 with the wraps 902-908 without using Bragg gratings whereseparate fibers separate wraps fiber 710 around thepipe 14 due to pressure changes, such as Mach Zehnder or Michaelson Interferometric techniques, such as that described in U.S. Pat. No. 5,218,197, entitled “Method And Apparatus For The Non-Invasive Measurement Of Pressure Inside Pipes Using A Fiber Optic Interferometer Sensor,” to Carroll. - The interferometric wraps may be multiplexed such as is described in Dandridge, et al, “Fiber Optic Sensors for Navy Applications,” IEEE, February 1991, or Dandridge, et al, “Multiplexed Interferometric Fiber Sensor Arrays,” SPIE, Vol. 1586, 1991, pp. 176-183. Other techniques to determine the change in fiber length may be used. Also, reference optical coils (not shown) may be used for certain interferometric approaches and may also be located on or around the
pipe 14 but may be designed to be insensitive to pressure variations. - Referring to FIGS. 27 and 28, instead of the wraps902-908 being optical fiber coils wrapped completely around the
pipe 14, the wraps 902-908 may have alternative geometries, such as a “radiator coil” geometry (FIG. 27) or a “race-track” geometry (FIG. 28), which are shown in a side view as if thepipe 14 is cut axially and laid flat. In this particular embodiment, the wraps 902-908 are not necessarily wrapped 360 degrees around the pipe, but may be disposed over a predetermined portion of the circumference of thepipe 14, and have a length long enough to optically detect the changes to the pipe circumference. Other geometries for the wraps may be used if desired. Also, for any geometry of the wraps described, more than one layer of fiber may be used depending on the overall fiber length desired. The desired axial length of any particular wrap is set depending on the characteristics of the ac pressure desired to be measured, for example the axial length of the pressure disturbance caused by a vortex to be measured. Referring to FIGS. 29 and 30, embodiments of the present invention include configurations wherein instead of using the wraps 902-908, thefiber 900 may have shorter sections that are disposed around at least a portion of the circumference of thepipe 14 that can optically detect changes to the pipe circumference. It is further within the scope of the present invention that sensors may comprise anoptical fiber 900 disposed in a helical pattern (not shown) aboutpipe 14. As discussed above, the orientation of the strain sensing element will vary the sensitivity to deflections in pipe wall 952 caused by unsteady pressure transients in thepipe 14. - Referring to FIG. 29, in particular, the pairs of Bragg gratings (910, 912), (914, 916), (918, 920), (922, 924) are located along the
fiber 900 with sections 980-986 of thefiber 900 between each of the grating pairs, respectively. In that case, known Fabry Perot, interferometric, time-of-flight or fiber laser sensing techniques may be used to measure the strain in the pipe, in a manner similar to that described in the aforementioned references. - Referring to FIG. 30, alternatively, individual gratings970-976 may be disposed on the pipe and used to sense the unsteady variations in strain in the pipe 14 (and thus the unsteady pressure within the pipe) at the sensing locations. When a single grating is used per sensor, the grating reflection wavelength shift will be indicative of changes in pipe diameter and thus pressure.
- Any other technique or configuration for an optical strain gage may be used. The type of optical strain gage technique and optical signal analysis approach is not critical to the present invention, and the scope of the invention is not intended to be limited to any particular technique or approach.
- The present invention will also work over a wide range of oil/water/gas mixtures. Also, the invention will work for very low flow velocities, e.g., at or below 1 ft/sec (or about 20.03 gal/min, in a 3 inch diameter ID pipe) and has no maximum flow rate limit. Further, the invention will work with the
pipe 14 being oriented vertical, horizontal, or any other orientation. Also the invention will work equally well independent of the direction of the flow along thepipe 14. - The thickness and rigidity of the outer wall of the
pipe 14 is related to the acceptable spacing X1 (FIG. 1) between thesensors spatial filter 733. More specifically, the thinner or less rigid thepipe 14 wall, the closer thesensors - Also, for optimal performance, the distance X1 between the two
sensors vortical pressure field 715 such that each of thesensors vortical pressure field 715 between thesensors spatial filter 733 output is not zero for the measured vortex 715). Also, the distance X1 should be within the coherence length of thevortex 715 such that the spatial filter output is indicative of a measuredvortex 715. Also, for optimal performance, the overall length L1 between thefirst sensor 718 and thelast sensor 724 of the velocity sensing section should be within the coherence length of thevortices 715 desired to be measured. The coherence length of thevortical flow field 715 is the length over which the vortical flow field remains substantially coherent, which is related to and scales with the diameter of thepipe 14. - Vortices that are sensed by only one of the spatial filters, because either a vortex is generated between the spatial filters or generated outside the spatial filters and decay between them, will be substantially random events (in time and location) that will not be correlated to the vortices that are sensed by and continuously occurring past both spatial filters and, as such, will not significantly affect the accuracy of the measurement.
- FIG. 31 illustrates an embodiment of a velocity measurement system in an oil or gas well application. The
sensing section 710 may be connected to or part ofproduction tubing 502 within a well 500. An outer housing, sheath, or cover 522 may be located over the sensors 718-724 and attached to the pipe (not shown) at the axial ends to protect the sensors 718-724 (or fibers) from damage during deployment, use, or retrieval, and/or to help isolate the sensors from external pressure effects that may exist outside thepipe 14, and/or to help isolate ac pressures in thepipe 14 from ac pressures outside thepipe 14. - The sensors718-724 are connected to a
cable 506 which may comprise the optical fiber 900 (FIG. 16) and is connected to a transceiver/converter 520 located outside the well. - When optical sensors are used, the transceiver/
converter 520 may be used to receive and transmit optical signals to the sensors 718-724 and provides output signals indicative of the pressure P1-P4 at the sensors 18-24 on the lines 730-736, respectively. - Also, the transceiver/
converter 520 may be part of theVelocity Logic 740. The transceiver/converter 520 may be any device that performs the corresponding functions described. In particular, the transceiver/converter 520 together with the optical sensors described hereinbefore may use any type of optical grating-based measurement technique, e.g., scanning interferometric, scanning Fabry Perot, acousto-optic-tuned filter (AOTF), optical filter, time-of-flight, etc., having sufficient sensitivity to measure the ac pressures within the pipe, such as that described in one or more of the following references: A. Kersey et al., “Multiplexed Fiber Bragg Grating Strain-Sensor System With A Fabry-Perot Wavelength Filter,” Opt. Letters, Vol. 18, No. 16, August 1993; U.S. Pat. No. 5,493,390, issued Feb. 20, 1996 to Mauro Verasi, et al.; U.S. Pat. No. 5,317,576, issued May 31, 1994, to Ball et al.; U.S. Pat. No. 5,564,832, issued Oct. 15, 1996 to Ball et al.; U.S. Pat. No. 5,513,913, issued May 7, 1996, to Ball et al.; U.S. Pat. No. 5,426,297, issued Jun. 20, 1995, to Dunphy et al.; U.S. Pat. No. 5,401,956, issued Mar. 28, 1995 to Dunphy et al.; U.S. Pat. No. 4,950,883, issued Aug. 21, 1990 to Glenn; U.S. Pat. No. 4,996,419, issued Feb. 26, 1991 to Morey, all of which are incorporated by reference. Also, the pressure sensors described may operate using one or more of the techniques described in the aforementioned references. - C. Other Velocity Measurement Techniques
- U.S. patent application Ser. No. 09/729,994, entitled “Method And Apparatus For Determining The Flow Velocity Within A Pipe,” filed Dec. 4, 2000, discloses an alternative method for determining the velocity of a fluid within a pipe, and is incorporated herein by reference in its entirety.
- III. Determining Flow Rates of Components in a Multiphase Mixture
- The present disclosure is not only useful in determining phase fractions (i.e. the quantity of each phase) in a fluid mixture, but is also useful in determining phase flow rates (i.e. the speed at which each phase flows in the mixture) by incorporating speed of sound measurements into a typical multiphase flow model. Multiphase flow models have been used in the past with distributed pressure and temperature measurements to determine phase flow rates as demonstrated in Nerby, et al., “Cost Effective Technique for Production Testing,” (1995) Offshore Technology Conference in Houston, U.S.A., pp.505-515, incorporated herein by reference in its entirety. A specific multiphase flow model is not needed for the present invention; any well-known multiphase flow models may be used. Therefore, the model itself will be described below in somewhat general terms as the exact methods differ between available models. The model itself is not the novel feature of the present invention; instead, it is the incorporation of a fluid sound speed measurement into the model, which provides a more accurate determination of phase flow rates.
- Multiphase flow models incorporating only pressure and temperature measurements have difficulty in predicting phase flow rates. This may largely result from the temperature measurement, because experience has shown that temperature remains difficult to measure accurately. Without accurate measurements the model cannot accurately describe the fluid. Furthermore, if temperature is used in the error function of the flow model (Eq. 22, discussed below), a description of the overall heat transfer characteristics of the well is necessary but, unfortunately, difficult to establish. Another problem appears, which is discussed in detail below, when evaluating the error function of the phase flow rates; namely multiple local minima appear. As one skilled in the art would know, error functions exhibiting many local minima make it difficult to find the true solution. Incorporating fluid sound speed into known multiphase flow models significantly increases the capability of a model to predict phase flow rates.
- FIG. 32 illustrates a single zone application of a multiphase flow measurement system according to the present invention. A
production pipe 14 extends from the reservoir to theplatform 54. Aflow meter 1006 is connected to theproduction pipe 14 approximately 100 meters or further from thewellhead 55. As one skilled in the art will realize, the depth at which gas comes out of solution largely determines this distance, although this distance can vary depending on the application. As an illustrative example and a rough guideline and depending on flow parameters, typical hydrocarbon and water mixtures remain in the bubbly flow regime at approximately 15% to 30% gas fraction for mixture flow rates >5 ft/sec in nearly vertical flows and at pressures of greater than approximately 3000 psi. For gas fractions above this level, bubbles tend to coalesce and the flow transitions to a slugging flow. From a multiphase flow measurement perspective, nearly homogenous flows, such as liquid or bubbly, are more straightforward to measure. The non-homogenous flows such as the slugging, churning, and annular flow are more challenging. - The
flow meter 1006 consists of two subassemblies, apressure assembly 1002 and aflow assembly 1004 separated by a short length of pipe called a pup joint 1008. Each assembly has separatefiber optic cables 52 for sending and receiving light to interrogate sensors within the subassemblies. The pup joint 1008 measures about 5 to 10 feet in length. It is desired to design the pup joint as short as possible so that the axial location of thepressure assembly 1002 and theflow assembly 1004 is effectively the same for measurement purposes, which is particularly true when one considers that production pipes can reach depths of thousands of feet. - The
pressure assembly 1002 and theflow assembly 1004 each have standardpremium thread connectors 1003 to attach to astandard pipe 14 such as 3.5 inch diameter production tubing. Thepressure assembly 1002 is about 5 feet in length and contains a 15,000-psi pressure and temperature transducer, such as the sensor apparatus disclosed in U.S. Pat. No. 6,016,702, entitled “High Sensitivity Fiber Optic Pressure Sensors For Use In Harsh Environments,” which is incorporated by reference in its entirety. Theflow assembly 1004 measures about 12 feet in length and contains a fiber optic velocity and a sound speed sensor, such as those described above in detail. The diameter of each assembly typically measures 5.60 inches because a protective housing surrounds the sensors, as is known. - As shown in FIG. 32, a
sensor 1010 located below thechoke valve 58 measures wellhead pressure and/or temperature. As one skilled in the art would realize, thesensor 1010 may be located on either side or on both sides of thechoke valve 58. Furthermore, thesensor 1010 may comprise an electrical strain gauge or an optical fiber sensor. For themodel 16 to determine phase flow rates, thesensor 1010 is located at a spatially removed location from theflow meter 1006. Locating thesensor 1010 in a vertically removed location from theflow meter 1006 insures that the pressure gradient between thesensor 1010 and thepressure assembly 1002 varies sufficiently in order to calculate a difference in pressure., If the difference in these pressures is negligible, the model may not accurately predict phase flow rates. - The data from the
pressure assembly 1002 and theflow assembly 1004 travels through eachfiber optic cable 52 from itsrespective connector region 1005 to theinstrumentation unit 56. Standard clamps 1012, such as LaSalle clamps, secure thecable 52 to thepipe 14. Theclamp 1012 may further secure other cable lines such as methanol injection lines and/or a subsurface safety valve lines, or other lines as is known in the art. As is well known, thefiber optic cable 52 may include a protection sheath that surrounds and protects the raw optical fiber within it. - The
instrumentation unit 56, as is well known, preferably consists of an optical light source, an opto-electronic interrogation unit, a signal demodulation unit, a microprocessor, monitor, keyboard, associated power supplies, disk drives, data communication interfaces, themultiphase flow model 16 software and other necessary items. Any type of a multiphase flow model may be used including, but not limited to, flow model software manufactured by ABB Ltd. of Zurich, Switzerland, or Idun software systems from FMC Kongsberg SubSea of Houston, Tex./Kongsberg, Norway. - When the
instrumentation unit 56 receives the data, themodel 16 predicts the phase flow rates in the basic manner depicted by FIG. 33. Theflow model 16 preferably begins atstep 70 where the fluid is defined thermodynamically, such as with a pressure measurement Pref and/or a temperature measurement Tref. However in place of measuring these parameters, they may instead be estimated and entered into themodel 16. In the embodiment shown in FIG. 32, thepressure assembly 1002 provides Pref and Tref to theinstrumentation unit 56. Thenext step 71 then makes a determination of “slippage” in the fluid. If a fluid has minimal slippage or no slippage, all phases within the fluid are flowing at basically the same rate and the initial estimation of individual phase flow rates is considerably less complicated. Fluid with minimal slippage typically has a high flow rate and occurs in a vertically inclined pipe, which is a typical scenario in an oil/gas well. The predicted phase flow rates for a minimal slippage fluid may be calculated from the following: - Q i=φi Av meas Eq. 20
- where subscript i represents the phase evaluated, Q is the predicted phase flow rate, φ is the phase fraction of the i phase of the fluid from the speed of sound sensor, as described in detail above, A is the cross-sectional area of the
pipe 14 and v is the measured velocity of the fluid mixture from the velocity sensor, as described in detail above. As one of skill in the art would know, if the fluid has three or more flowing phases, the phase fractions φ of the fluid mixture possibly cannot be directly determined from the speed of sound sensor, and instead the model makes an iterative determination of the phase fractions. By knowing the phase fractions, area of the pipe and velocity of the fluid mixture, the phase flow rates for a fluid mixture with minimal slippage is initially determined instep 72. - If the fluid exhibits a slippage condition, then the model will estimate (as opposed to calculate) the initial phase flow rates in
step 73. This estimation varies between models, but generally, the basic information of the fluid, pipe geometry, the path fluid travels, constrictions within the pipe, and other factors known in the art are evaluated. As one skilled in the art would realize, the results of a good multiphase flow model do not depend on the accuracy of the predicted phase flow rates. Instead, by the error minimization process described below any predicted flow rate should eventually lead to the true flow rate after several iterations through the error function (Eq. 22 below). - After the initial determination of phase flow rates, the
model 16 can calculate, instep 74, any flow-related parameter as long as the proper transfer function is known. The transfer function is the basic mathematical calculations for calculating a parameter, such as sound speed, from the estimated phase flow rates using well understood principles of fluid dynamics (SOS=f|Qo, Qg, Qw|). These calculated parameters are then compared to the actual measured parameters, e.g., the fluid mixture sound speed from the speed of sound meter in theflow assembly 1004. Themodel 16 requires at a minimum one measurement for every phase flowing in the fluid 12 in addition to the preferable starting point measurements, i.e. Pref and Tref. Thus a two-phase oil/water fluid would require two additional measurements as well as the Pref and/or Tref, and likewise an oil/water/gas fluid requires three additional measurements as well as the Pref and/or Tref. The additional measurements include fluid sound speed and at a minimum, either pressure, temperature, velocity or an additional fluid sound speed. - As stated previously, it is already known in the art to utilize parameters such as pressure, temperature, and velocity with a multiphase flow model to determine phase flow rates. However, the present invention incorporates the parameter of fluid sound speed into the
model 16. This significantly increases the accuracy of themodel 16, as will be shown below. Accordingly instep 74 sound speed is calculated through known transfer functions, as previously noted, another one or two parameters (depending on the number of phases) such as pressure, temperature and/or velocity is likewise calculated. These calculated parameters are then compared to the corresponding measured parameters as indicated bystep 75. For the embodiment depicted in FIG. 32, the corresponding measurement parameters would include fluid sound speed and velocity from theflow assembly 1004 and wellhead pressure and/or temperature fromsensor 1010. The comparison is then evaluated through an error function in step 76 (Eq. 22) which will be described in more detail below. - A simplified example may help illustrate the basic method behind multiphase flow models. One will realize that the pressure of a fluid within a vertical pipe decreases as one measures from the bottom of the well to the
well head 55. The model, starting from the Pref starting point, essentially calculates the pressure drop at successive, rising intervals along thepipe 14 in accordance with the following equation: - where Q is the estimated flow rate of the mixture, A is the cross sectional area of the pipe, ρ is the density of the fluid mixture which can be measured or estimated by known methods, k is a known discharge coefficient, and P1 is the pressure at the starting point, which initially is equal to Pref. The model calculates a P2 at successive intervals until it estimates a pressure drop calculation at the
well head 55, Pwh. The model then compares this estimated Pwh with the actual Pwh measurement from thepressure sensor 1010. The amount of error between the two results is analyzed by the error function (Eq. 22). The result then leads the model to choose corresponding phase flow rates (step 77) and the process begins again. The process will repeat itself until the error is within acceptable limits and the results are then taken as the true phase flow rates and stored instep 78. - As shown above, Eq. 21 estimates the mixture flow rate Qw, not the individual flow rates, thus one may wonder as to how this equation may help in determining the individual flow rates. What Eq. 21 does provide, however, is an additional constraint to the model, which enables the model to determine the individual component flow rates. It, by itself, would not be sufficient to determine component flow rates, but, in conjunction with the other constraints, such as measured mixture sound speed, it adds yet another constraint into the optimization process and improves the ability of the overall optimization of determining component flow rates.
- The process described above, although illustrative, is a simplistic example of how the model determines phase flow rates. Depending on the multiphase flow model chosen the process may further take into consideration certain parameters to accurately depict the well conditions. Parameters that many models include are well geometry (horizontal, vertical or angled sections), the true vertical depth, ambient temperature along the fluid path, heat properties for the well formation, phase densities, viscosity and surface tension, pipe wall friction and the gas-oil ratio at equilibrium. These physical parameters are incorporated into the transfer functions to make the parameter calculations.
- As mentioned several times above, the multiphase model couples to an error function to continually narrow the initial estimated phase flow rates to arrive at the correct solution. What has been discovered is that by incorporating fluid sound speed into this standard error function the accuracy of the predicted phase flow rates significantly improves. The standard error function is formulated as:
- where j represents the parameter at issue (e.g. sound speed), W is a user defined weight factor for that parameter, and Xm and Xc are the measured and corresponding calculated parameters respectively. By virtue of the summation, this single equation incorporates all of the error terms of all parameters of interest, including fluid sound speed. If the results fall within a designated error range, for example 5%, then the phase flow rates reflect the true phase flow rates of the components in the fluid mixture. However, if the error exceeds the error range then the
model 16 performs a new vector search as indicated bystep 77 and the process begins again. - The improvement in the performance of the optimization procedure resulting from the incorporation of sound speed measurement is a result of the direct physical link between mixture sound speed and flow composition (
equations 16 and 17). This constraint penalizes solutions that may satisfy other constraints, but does not constitute physically-accurate solutions. For example, given a pressure change from one location in a well to another, and assuming this to be the only measurement information available, a multiphase flow solution might be unable to determine whether the pressure drop resulted from a dense fluid moving slowly, or a light fluid flowing quickly, resulting in what is often referred to as “multiple, equi-probable solutions.” In other words, the measurements are not sufficient to uniquely determine composition and flow rate. However, using a sound speed measurement in conjunction with a pressure differential constrains the optimization such that only one, unique solution minimizes the optimization. Constraining the sound speed of the mixture thus, in effect, predominately determines the density, allowing the pressure measurement to predominately determine the mixture flow rate. - In a numerical study performed of a three-phase fluid (oil/gas/water) comparing a prior art system using pressure and temperature measurements with the invention incorporating sound speed measurements, the study demonstrated the significant improvement in predicting phase flow rates when sound speed calculations are used. The prior art pressure/temperature system consisted of a pressure/temperature measurement downhole with a pressure/temperature measurement both below and above the
choke valve 58. The speed of sound system corresponded to the embodiment shown in FIG. 32 with a speed of sound, velocity, pressure and temperature measurement downhole and a pressure measurement below thechoke valve 58. - As demonstrated by FIGS. 34 and 35, the
model 16 for the pressure/temperature system was not able to reproduce the correct phase flow rates within a desired +/−5% error range. Both FIGS. 34 and 35 represent a fluid with a gas/oil ratio (GOR) of 200 with Fis. 34 representing oil rate (Qo) and FIG. 35 representing water rate (Qw). The error range of +/−5% is depicted in the graph as two horizontal lines. The total liquid flow rate extends along the x-axis with units of Sm3/D, which is standard meters3 per day. One may realize that the graphs show total liquid flow as opposed to the individual phase flow rates. This is preferred because the velocity sensor directly measures the total liquid flow measurement, while the model indirectly measures the individual phase flow rates. By graphing the total flow rate, the graphs become easily comparable to each other and the data is plotted by a direct measurement instead of a one step removed, indirect measurement. Furthermore, one of skill in the art will realize that if the total flow rate at a given point is multiplied with the point's representative phase fraction percent (100%-wc %), the desired individual phase flow rate (Qo, Qw, Qg) can be determined (taking into consideration the error percentage). - In FIGS. 34 and 35, many points fall outside of the 5% error range. In FIG. 34 several data points fall outside of the 50% and even 100% error range, clearly indicating how poorly the model predicts oil flow rates with pressure and temperature measurements alone. Turning to FIG. 35, the data significantly erodes with error percentages approaching 3500%. Furthermore, high watercuts such as 60% and 80% have some of the highest errors. As one of skill in the art may realize these watercuts should instead have the greatest accuracy, as will be discussed below.
- Turning to FIG. 36, establishing the value of the error function (from Eq. 22) based on one single pass through the search routine generated the data for FIG. 36. The error function is graphed for three GORs (150, 200, and 250). Again the total liquid flow rate is on the x-axis, watercut is on the y-axis and the error function is on the z-axis. As one will notice, the figure demonstrates that for a model incorporating temperature and pressure measurements alone, multiple
local minima 1020 appear for any set of parameters. For example with a GOR of 200, at least four local minima appear, effectively masking the true solution minimum 1022, which is shown at 4000 Sm3/D for a GOR of 200. Theselocal minima 1020 can mislead one to believe that thetrue minimum 1022 lies within reach, when in fact a local minimum is leading to the wrong result. - However, applying speed of sound to the
model 16 displayed significantly better results. FIGS. 37-39 depict a fluid with a GOR of 200. Again two bold lines depict the +/−5% error range and for FIG. 37 (Gas Rate) and FIG. 38 (Oil Rate) nearly every point representing a specific watercut percentage falls within the acceptable range of error. The graphs therefore demonstrate the beneficial effect of incorporating speed of sound with velocity and pressure into a multiphase flow model. - One will notice that with regard to FIG. 39, Water Rate points representing small percentages of watercut have larger deviations from the correct value. These larger deviations (which are still significantly below the error of 2000-3500% in FIG. 35) however only appear in watercut percentages of less than 10%. As one skilled in the art would realize, this is of little consequence. When dealing with error percentages, very small flow rates will exhibit magnified errors and thus acceptance criteria based on relative error alone, as shown in FIG. 39, leads to exaggerated deviations. Instead, acceptance criteria should be formulated as a combination of relative and absolute values, and when the data of FIG. 39 is subjected to that criterion, the results fall within the standard range of error. A simplified example, though, may be helpful. If an oil/water fluid has a total flow rate of 1000 barrels/day and phase fractions of 96% oil and 4% water and a margin of error of +/−5%, the oil flows at about 960 barrels/day with an error range of 50 barrels (910 to 1010 barrels/day). However, the water would be flowing at only 40 barrels/day (1000×0.04). The error of 50 barrels a day becomes quite significant, ranging from −10 to 90 barrels/day. Hence a relatively small error percentage becomes increasingly magnified with smaller flow rates. Thus when small flow rates are present, the acceptance criteria should be based on a combination of relative and absolute values as is known. And referring back to FIG. 35, incorporating only pressure and temperature measurements led to significant errors in watercuts with high percentages. This again demonstrates the improvement of incorporating sound speed into a multiphase flow model.
- Now turning to FIG. 40 one will notice that instead of many local minima, the graph indicates only a single
true minimum 1022 for a GOR of 200, at approximately 4000 Sm3/D. (The GOR error function for 150 is not shown as the surface dimensions were out of scale with respect to the z-axis.) Further, the steep slope of the error function quickly leads one to the correct result. FIG. 40 demonstrates again the improvement of models incorporating sound speed. Once the model has reached the true minimum, the model stores the results instep 78. - Now referring to FIG. 41 there is shown a multizone,
multiphase production system 50 having distributed temperature andpressure transducers 32 located at various axial positions alongpipe 14. Thesystem 50 further comprises multiple distributedsensor apparatuses 33 located at various axial positions alongpipe 14 providing temperature, pressure, speed of sound and/or bulk velocity of the fluid at each location. This embodiment has taken FIG. 32 and distributed the basic configuration over many locations. This configuration is more complicated than that described above but derives benefits of combining distributed measurement systems with distributed sound speed and velocity measurements. Each sensor produces a signal communicated to themodel 16 viacable 52 located at theplatform 54 or a remote location. In the case of multi-zone distributed sensor systems, it is more difficult, and less meaningful, to attempt to isolate the role of each constraint in the overall optimization system. However, utilizing fully distributed sound speed, velocity, pressure and temperature measurements enables one to address systems of arbitrary complexity. In this optimization, all relationships linking the distributed measurements to the desired quantities can and should be exploited. - As stated previously, the sensors may comprise any type of sensor capable of measuring the unsteady (or ac or dynamic) pressures within a pipe, such as piezoelectric, optical, capacitive, resistive (e.g., Wheatstone bridge), accelerometers (or geophones), velocity measuring devices, displacement measuring devices, etc. If optical pressure sensors are used, the sensors may be Bragg grating based pressure sensors, such as that described in U.S. Pat. No. 6,016,702, entitled “High Sensitivity Fiber Optic Pressure Sensor For Use In Harsh Environments.” Alternatively, the sensors may be electrical or optical strain gauges attached to or embedded in the outer or inner wall of the pipe and which measure pipe wall strain, including microphones, hydrophones, or any other sensor capable of measuring the unsteady pressures within the pipe. In an embodiment of the present invention that utilizes fiber optics as the pressure sensors the pressure sensors may be connected individually or may be multiplexed along one or more optical fibers using wavelength division multiplexing (WDM), time division multiplexing (TDM), or any other optical multiplexing techniques. Alternatively, a portion or all of the fiber between the gratings (or including the gratings, or the entire fiber, if desired) may be doped with a rare earth dopant (such as erbium) to create a tunable fiber laser, such as is described in U.S. Pat. No. 5,317,576, entitled “Continuously Tunable Single Mode Rare-Earth Doped Laser Arrangement,” to Ball et al., or U.S. Pat. No. 5,513,913, entitled “Active Multipoint Fiber Laser Sensor,” to Ball et al., or U.S. Pat. No. 5,564,832, entitled “Birefringent Active Fiber Laser Sensor,” to Ball et al., all of which are incorporated herein by reference.
- For any of the embodiments described, the pressure sensors, including electrical strain gauges, optical fibers and/or gratings among others as described, may be attached to the pipe by adhesive, glue, epoxy, tape or other suitable attachment means to ensure suitable contact between the sensor and the pipe. The sensors may alternatively be removable or permanently attached via known mechanical techniques such as by mechanical fastener, by a spring loaded arrangement, by clamping, by a clam shell arrangement, by strapping or by other equivalents. Alternatively, the strain gauges, including optical fibers and/or gratings, may be embedded in a composite pipe. If desired, for certain applications, the gratings may be detached from (or strain or acoustically isolated from) the pipe if desired.
- The present invention allows the speed of sound to be determined in a pipe independent of pipe orientation, i.e., vertical, horizontal, or any other orientation. Also, the invention does not require any disruption to the flow within the pipe (e.g., an orifice or venturi). Further, the invention may use ac (or unsteady or dynamic) pressure measurements as opposed to static (dc) pressure measurements and is therefore less sensitive to static shifts (or errors) in sensing. Furthermore, if harsh environment fiber optic pressure sensors are used to obtain the pressure measurements, such sensors eliminate the need for any electronic components down-hole, thereby improving reliability of the measurement.
- In the embodiments shown and discussed, some or all of the functions within the
model 16 and/or Logic (140, 160, 740) may be implemented in software (using a microprocessor or computer) and/or firmware, or may be implemented using analog and/or digital hardware, having sufficient memory, interfaces, and capacity to perform the functions described. - It should be understood that any of the features, characteristics, alternatives or modifications described regarding a particular embodiment may also be applied, used, or incorporated with any other embodiment described.
- Although the invention has been described and illustrated with respect to exemplary embodiments thereof, the foregoing and various other additions and omissions may be made therein and thereto without departing from the spirit and scope of the present invention.
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